Liquid fuel compositions

ABSTRACT

A moderate fraction of a carbohydrate derived component, and a kerosene composition comprising the moderate fraction, the moderate fraction having at least one C 4+  compound, wherein:
     the moderate fraction exhibits:
       a mean percentage of 99% or more biobased material, as determined by C 14  testing; and,   a final boiling point in the range of from 200 to 320° C.; and,   the moderate fraction comprises:
           a first quantity of one or more branched carbohydrate derived C 4+  alkanes;   a second quantity of one or more straight chain carbohydrate derived C 4+  alkanes;   
           
       a concentration of one or more substituted carbohydrate derived C 5+  cycloalkanes comprising substituents selected from the group consisting of branched C 3-4  alkyls and straight chain C 1-4  alkyls, at least some of the substituted carbohydrate derived C 5+  cycloalkanes comprising fused cycloalkanes.

The present application is a divisional of U.S. application Ser. No. 12/553,212 (currently pending), which claims the benefit of U.S. Provisional Application Ser. No. 61/094,482, filed Sep. 5, 2008, the entire disclosure of which is hereby incorporated by reference.

FIELD OF THE INVENTION

The present invention relates to liquid fuel compositions comprising a component derived from a water-soluble oxygenated hydrocarbon.

BACKGROUND OF THE INVENTION

Significant amount of attention has been placed on developing new technologies for providing energy from resources other than fossil fuels. Biomass is a resource that shows promise as a fossil fuel alternative. As opposed to fossil fuel, biomass is also renewable.

One type of biomass is plant biomass. Plant biomass is the most abundant source of carbohydrate in the world due to the lignocellulosic materials composing the cell walls in higher plants. Plant cell walls are divided into two sections, primary cell walls and secondary cell walls. The primary cell wall provides structure for expanding cells and is composed of three major polysaccharides (cellulose, pectin, and hemicellulose) and one group of glycoproteins. The secondary cell wall, which is produced after the cell has finished growing, also contains polysaccharides and is strengthened through polymeric lignin covalently cross-linked to hemicellulose. Hemicellulose and pectin are typically found in abundance, but cellulose is the predominant polysaccharide and the most abundant source of carbohydrates.

Most transportation vehicles, whether boats, trains, planes and automobiles, require high power density provided by internal combustion and/or propulsion engines. These engines require clean burning fuels which are generally in liquid form or, to a lesser extent, compressed gases. Liquid fuels are more portable due to their high energy density and their ability to be pumped, which makes handling easier.

Currently, biomass provides the only renewable alternative for liquid transportation fuels. Unfortunately, the progress in developing new technologies for producing liquid biofuels has been slow in developing, especially for liquid fuel products that fit within the current infrastructure. Although a variety of fuels can be produced from biomass resources, such as ethanol, methanol, biodiesel, Fischer-Tropsch diesel and kerosene, and gaseous fuels, such as hydrogen and methane, these fuels can require either new distribution technologies and/or combustion technologies appropriate for their characteristics. The production of these fuels also tends to be expensive.

Ethanol, for example, is made by converting the carbohydrate from biomass into sugar, which is then converted into ethanol in a fermentation process. Ethanol is the most widely used biofuel today with current capacity of 4.3 billion gallons per year based on starch crops, such as corn. Ethanol, however, has very substantial disadvantages with respect its energy value as a fuel relative to the amount of energy needed to produce it. Ethanol produced by fermentation contains large amounts of water, typically comprising only about 5 percent of ethanol by volume in the water/alcohol fermentation product. The removal of this water is highly energy-consuming, and often requires the use of natural gas as a heat source. Ethanol also has less energy content than gasoline, which means that it takes more fuel to go the same distance. Ethanol is very corrosive to fuel systems and cannot be transported in petroleum pipelines. As a result, ethanol is transported over-the-road in tank trucks, which increases its overall cost and energy consumption. When considering the total energy consumed by farm equipment, cultivation, planting, fertilizers, pesticides, herbicides, petroleum-based fungicides, irrigation systems, harvesting, transportation to processing plants, fermentation, distillation, drying, transport to fuel terminals and retail pumps, and lower ethanol fuel energy content, the net energy content value added and delivered to consumers is very small.

Biodiesel is another potential energy source. Biodiesel can be made from vegetable oil, animal fats, waste vegetable oils, microalgae oils or recycled restaurant greases, and is produced through a process in which organically derived oils are combined with alcohol (ethanol or methanol) in the presence of a catalyst to form ethyl or methyl ester. The biomass-derived ethyl or methyl esters can then be blended with conventional diesel fuel or used as a neat fuel (100% biodiesel). Biodiesel is also expensive to manufacture, and poses various issues in its use and combustion. For example, special handling may be required to avoid gelling in cold temperatures.

Biomass can also be gasified to produce a synthesis gas composed primarily of hydrogen and carbon monoxide, also called syngas or biosyngas. Syngas produced today is used directly to generate heat and power, but several types of biofuels may be derived from syngas. Hydrogen can be recovered from syngas, or it can be catalytically converted to methanol. The gas can also be run through a biological reactor to produce ethanol or converted using Fischer-Tropsch catalyst into a liquid stream with properties similar to diesel fuel, called Fischer-Tropsch diesel. These processes, however, tend to be expensive.

There exists a need for liquid fuel compositions which contain a component that is derivable from biomass and that is capable of use in the current infrastructure, namely the same distribution system and the same engines without the need for special modifications. There also exists a need for liquid fuel compositions which contain a component that is derivable from biomass that do not depend on microorganisms, enzymes or other expensive and delicate manufacturing processes.

SUMMARY OF THE INVENTION

In one embodiment, the application provides a moderate fraction of a carbohydrate derived component having at least one C₄₊ compound, wherein:

-   -   the moderate fraction exhibits:         -   a mean percentage of 99% or more biobased material, as             determined by C₁₄ testing; and,         -   a final boiling point in the range of from 200 to 320° C.;             and,     -   the moderate fraction comprises:         -   a first quantity of one or more branched carbohydrate             derived C₄₊ alkanes;         -   a second quantity of one or more straight chain carbohydrate             derived C₄₊ alkanes;         -   a concentration of one or more substituted carbohydrate             derived C₅₊ cycloalkanes comprising substituents selected             from the group consisting of branched C₃₋₄ alkyls and             straight chain C₁₋₄ alkyls, at least some of the substituted             carbohydrate derived C₅₊ cycloalkanes comprising fused             cycloalkanes.

In one embodiment, the application provides a kerosene composition comprising:

-   -   a moderate fraction of a carbohydrate derived component having         at least one C₄₊ compound having a mean percentage of 99% or         more biobased material, as determined by C₁₄ testing, the         moderate fraction having a final boiling point in the range of         from 200 to 320° C.;     -   the moderate fraction comprising:         -   a first quantity of one or more branched carbohydrate             derived C₄₊ alkanes;         -   a second quantity of one or more straight chain carbohydrate             derived C₄₊ alkanes;         -   a concentration of one or more substituted carbohydrate             derived C₅₊ cycloalkanes comprising substituents selected             from the group consisting of branched C₃₋₄ alkyls and             straight chain C₁₋₄ alkyls, at least some of the substituted             carbohydrate derived C₅₊ cycloalkanes comprising fused             cycloalkanes;     -   the kerosene composition having a final boiling point in the         range of from 200 to 320° C. and a viscosity at −20° C. in the         range of from 0.8 to 10 cSt (ASTM D445).

In one embodiment, the application provides a kerosene composition comprising:

-   -   a moderate fraction of a carbohydrate derived component having         at least one C₄₊ compound having a mean percentage of 99% or         more biobased material, as determined by C₁₄ testing, the         moderate fraction having a final boiling point in the range of         from 200 to 320° C.;     -   the moderate fraction comprising:         -   a first quantity of one or more branched carbohydrate             derived C₄₊ alkanes;         -   a second quantity of one or more straight chain carbohydrate             derived C₄₊ alkanes;         -   a concentration of one or more substituted carbohydrate             derived C₅₊ cycloalkanes comprising substituents selected             from the group consisting of branched C₃₋₄ alkyls and             straight chain C₁₋₄ alkyls, at least some of the substituted             carbohydrate derived C₅₊ cycloalkanes comprising fused             cycloalkanes;     -   one or more different kerosene blend components comprising a         synthetic paraffin comprising components having boiling points         within the range of from 110 to 320° C.;     -   the kerosene composition having a final boiling point in the         range of from 200 to 320° C. and a viscosity at −20° C. in the         range of from 0.8 to 10 cSt (ASTM D445).

BRIEF DESCRIPTION OF THE DRAWINGS

FIG. 1 is a flow diagram illustrating various production pathways associated with the present invention.

FIG. 2 illustrates potential chemical routes that allow carbohydrates, such as sugars, to be converted to non-oxygenated hydrocarbons.

FIG. 3 is an illustration of various reaction pathways involved in the deoxygenation of sorbitol to oxygenates and APR hydrogen.

FIG. 4 is an illustration of the thermodynamic equilibriums along the reaction pathway for converting acetone to 2-methyl pentane at 100° C. and 400° C.

FIG. 5 is a graph illustrating the equilibrium constants associated with the intermediate reaction products and the overall conversion for the reaction of 2 moles of acetone with 3 moles of hydrogen to form 1 mole of 2-methylpentane and 2 moles of water.

FIG. 6 is a flow diagram illustrating a reactor system configured to allow for the recycle of hydrogen, oxygenates and oxygenated hydrocarbons.

FIG. 7 is a flow diagram illustrating a reactor system configured to allow for the use of air or an oil as a temperature control element.

FIG. 8 a flow diagram illustrating a reactor system for the present invention.

FIG. 9 is a flow diagram illustrating a reactor system utilizing two reactors.

FIG. 10 is a flow diagram illustrating a reactor system utilizing two feedstock lines.

FIG. 11 is an illustration of a reactor useful in practicing the present invention.

FIG. 12 is a graph illustrating the carbon distribution of mono-oxygenates produced from glycerol.

FIG. 13 is a graph illustrating the axial temperature profile for a reactor when used to produce compounds from a feedstock of oxygenated hydrocarbons.

FIG. 14 is a graph illustrating the percentage of feed carbon exiting as oxygenates from the conversion of an oxygenate feed stream to C₅₊ compounds as a function of time.

FIG. 15 is a graph illustrating the percentage of feed carbon exiting as C₅₊ hydrocarbons from the conversion of an oxygenate feed stream as a function of time.

FIG. 16 is a graph illustrating the percentage of feed carbon exiting as C₅₊ aromatic hydrocarbons from the conversion of an oxygenate feed stream as a function of time.

FIG. 17 is a graph showing the total weight percentage of paraffin and aromatic compounds derived from the conversion of a feed stream of sucrose and xylose.

FIG. 18 is a graph illustrating the heating value of C₅₊ hydrocarbons derived from the production of gasoline from sorbitol, as a percentage of the heating value of the feed.

FIG. 19 is a graph illustrating the percentage of carbon recovered as aromatic hydrocarbons from the production of gasoline from sorbitol, shown as a percentage of the carbon present in the feed.

DETAILED DESCRIPTION OF THE INVENTION

The liquid fuel compositions of the present invention comprise a component having at least one C₄₊ compound derived from a water-soluble oxygenated hydrocarbon. Preferably, the water-soluble oxygenated hydrocarbon is derived from biomass.

Typically, the process of preparing the component having at least one C₄₊ compound derived from a water-soluble oxygenated hydrocarbon produces hydrocarbons, ketones and alcohols from biomass-derived oxygenated hydrocarbons, such as sugars, sugar alcohols, cellulosics, lignocelluloses, hemicelluloses, saccharides and the like.

The component derived from a water-soluble oxygenated hydrocarbon comprises C₄₊ alkanes, C₄₊ alkenes, C₅₊ cycloalkanes, C₅₊ cycloalkenes, aryls, fused aryls, C₄₊ alcohols, C₄₊ ketones, and mixtures thereof (collectively referred to herein as “C₄₊ compounds”). The C₄₊ hydrocarbons typically have from 4 to 30 carbon atoms and may be branched or straight chained alkanes or alkenes, or unsubstituted, mono-substituted or multi-substituted aromatics (aryls) or cycloalkanes. The C₄₊ alcohols and C₄₊ ketones may be cyclic, branched or straight chained, and have from 4 to 30 carbon atoms.

Lighter fractions, primarily C₄-C₉, may be separated for gasoline use. Moderate fractions, such as C₇-C₁₄, may be separated for kerosene, for example for use in jet fuel, while heavier fractions, i.e., C₁₂-C₂₄, may be separated for diesel fuel use. The heaviest fractions may be used as lubricants or cracked to produce additional gasoline and/or diesel fractions. The C₄₊ compounds derived from water-soluble oxygenated hydrocarbons may also find use as industrial chemicals, such as xylene, whether as an intermediate or an end product.

Process of Preparing the Component Derived from a Water-Soluble Oxygenated Hydrocarbon

The general process of preparing the component derived from a water-soluble oxygenated hydrocarbon is illustrated in FIG. 1. A feedstock solution containing a water-soluble oxygenated hydrocarbon having one or more carbon atoms is reacted with hydrogen over a deoxygenation catalyst to produce oxygenates, and then the oxygenates are reacted over a condensation catalyst under conditions of temperature and pressure effective to cause a condensation reaction that produces the C₄₊ compounds. The hydrogen may originate from any source, but is preferably derived in situ or in parallel from biomass using aqueous phase reforming. The hydrogen and oxygenated hydrocarbons may also be supplemented with recycled hydrogen and oxygenated hydrocarbons derived from the process. The oxygenated hydrocarbon may be a monosaccharide, disaccharide, polysaccharide, cellulose, hemicellulose, lignin, sugar, sugar alcohol or other polyhydric alcohols, or may be derived from the hydrogenation of a sugar, furfural, carboxylic acid, ketone, or furan, or the hydrogenolysis of a sugar, sugar alcohol, polysaccharide, monosaccharide, disaccharide or polyhydric alcohol.

One unique aspect about the process of preparing the component derived from a water-soluble oxygenated hydrocarbon in the present invention is that the C₄₊ compounds are derived from biomass components using catalytic processes instead of microorganisms, enzymes, high temperature gasification or transesterification methods. The process of preparing the component derived from a water-soluble oxygenated hydrocarbon in the present invention can also generate hydrogen in situ to avoid reliance on external hydrogen sources, such as hydrogen generated from the steam reforming of natural gas, or the electrolysis or thermolysis of water. The process of preparing the component derived from a water-soluble oxygenated hydrocarbon in the present invention also generates water, which may be recycled and used in upstream processes or returned to the environment. The process of preparing the component derived from a water-soluble oxygenated hydrocarbon in the present invention is also able to generate non-condensable fuel gases for purposes of providing a heat source within the reactor system or for external processes.

Carbohydrates are the most widely distributed, naturally occurring organic compounds on Earth. Carbohydrates are produced during photosynthesis, a process in which the energy from the sun is converted into chemical energy by combining carbon dioxide with water to form carbohydrates and oxygen:

The energy from sunlight is stored through this process as chemical energy in the form of carbohydrates in plants. The carbohydrates, especially when in a sugar form, are highly reactive compounds that are readily oxidized by living material to generate energy, carbon dioxide and water. Plant materials store these carbohydrates either as sugars, starches, polymeric cellulose, and/or hemi-cellulose.

The presence of oxygen in the molecular structure of carbohydrates contributes to the reactivity of sugars in biological systems. Ethanol fermentation technology takes advantage of this highly reactive nature by forming ethanol at ambient temperatures. The fermentation technology essentially de-functionalizes the highly reactive sugar to generate a partially oxidized hydrocarbon, ethanol. Ethanol, however, has very substantial disadvantages with respect its energy value as highlighted above.

FIG. 2 shows potential chemical routes that allow carbohydrates, such as sugars, to be converted to non-oxygenated hydrocarbons. Water soluble carbohydrates are known to react with hydrogen over catalyst(s) to generate polyhydric alcohols, either by hydrogenation or hydrogenolysis. The hydrogen has historically been generated externally, i.e., from natural gas or by other processes, but can now be generated in situ or in parallel according to the present invention through the aqueous-phase reforming of the polyhydric alcohol.

The aqueous-phase reforming (APR) of the polyhydric alcohol proceeds through the formation of an aldehyde (shown in FIG. 2) where the aldehyde reacts over a catalyst with water to form hydrogen, carbon dioxide, and a smaller polyhydric alcohol. The polyhydric alcohol can further react with hydrogen over a catalyst through a series of deoxygenation reactions to form either alcohol, ketone, or aldehydes species that can undergo condensation reactions to form either larger carbon number straight chain compounds, branched chain compounds, or cyclic compounds. The condensation reactions can be either acid catalyzed, base catalyzed, or both acid and base catalyzed. The resulting compounds may be hydrocarbons or hydrocarbons containing oxygen, the oxygen of which can be removed through the reaction with hydrogen over a catalyst. The resulting condensed products include C₄₊ alcohols, C₄₊ ketones, C₄₊ alkanes, C₄₊ alkenes, C₅₊ cycloalkanes, C₅₊ cycloalkenes, aryls, fused aryls, and mixtures thereof. The mixtures can be fractionated and blended to produce the appropriate mixtures of molecules typically used in gasoline, kerosene (for example as jet fuel), or diesel fuels.

The de-functionalization begins by reacting the glucose with hydrogen in either a hydrogenation reaction or hydrogenolysis reaction to convert the cyclic sugar molecule to its corresponding linear alcohol, sorbitol, or lower polyhydric alcohols, such as glycerol, propylene glycol, ethylene glycol, xylitol, among others. As indicated above, the hydrogen may be from any source, but is preferably hydrogen generated in situ by aqueous phase reforming or excess hydrogen recycled from the reactor system.

During the aqueous phase reforming process, the carbohydrate first undergoes dehydrogenation to provide adsorbed intermediates, prior to cleavage of C—C or C—O bonds. Subsequent cleavage of C—C bonds leads to the formation of CO and H₂, with the CO then reacting with water to form CO₂ and H₂ by the water-gas shift reaction. Various APR methods and techniques are described in U.S. Pat. Nos. 6,699,457; 6,964,757 and 6,964,758; and U.S. patent application Ser. No. 11/234,727 (all to Cortright et al., and entitled “Low-Temperature Hydrogen Production from Oxygenated Hydrocarbons”); and U.S. Pat. No. 6,953,873 (to Cortright et al., and entitled “Low Temperature Hydrocarbon Production from Oxygenated Hydrocarbons”); and WO 2007/075476 A2 (to Cortright et al., and entitled “Catalyst and Methods for Reforming Oxygenated Compounds”), all of which are incorporated herein by reference. The term “aqueous phase reforming” and “APR” shall generically denote the reforming of oxygenated hydrocarbons and water to yield hydrogen and carbon dioxide, regardless of whether the reactions takes place in the gaseous phase or in the condensed liquid phase. “APR H₂” shall generically refer to the hydrogen produced by the APR process.

The resulting oxygenated hydrocarbon, namely the sorbitol or glycerol, propylene glycol, ethylene glycol, xylitol, etc., are further defunctionalized through deoxygenation reactions to form oxygenates, such as alcohols, ketones, aldehydes, furans, diols, triols, hydroxy carboxylic acids, and carboxylic acids for use in later condensation reactions. FIG. 3 illustrates various reaction pathways involved in the deoxygenation of sorbitol to oxygenates and APR hydrogen. In general, without being limited to any particular theory, it is believed that the deoxygenation reactions involves a combination of various different reaction pathways, including without limitation: hydrodeoxygenation, consecutive dehydration-hydrogenation, hydrogenolysis, hydrogenation and dehydration reactions, resulting in the removal of oxygen from the oxygenated hydrocarbon to arrive at a hydrocarbon molecule having the general formula C₁₊O₁₋₃.

The oxygenates produced are then converted into C₄₊ compounds by condensation. Without being limited to any specific theories, it is believed that the acid condensation reactions generally consist of a series of steps involving: (a) the dehydration of oxygenates to olefins; (b) oligomerization of the olefins; (c) cracking reactions; (d) cyclization of larger olefins to form aromatics; (e) paraffin isomerization; and (f) hydrogen-transfer reactions to form paraffins. Basic condensation reactions are believed to generally consist of a series of steps involving: (1) aldol condensation to form a β-hydroxyketone or β-hydroxyaldehyde; (2) dehydration of the β-hydroxyketone or β-hydroxyaldehyde to form a conjugated enone; (3) hydrogenation of the conjugated enone to form a ketone or aldehyde, which may participate in further condensation reactions or conversion to an alcohol or hydrocarbon; and (4) hydrogenation of carbonyls to alcohols, or vice-versa. Acid-base condensation reactions are believed to generally involve any of the previous acidic and/or basic reactions steps.

In certain embodiments, the condensation reactions occur at typical condensation temperatures and pressures. However, in various embodiments, it may also be more favorable to conduct the condensation reactions at temperature and/or pressure conditions that are elevated as compared to typical condensation processes. Generally, conducting condensation reactions under elevated conditions results in unfavorable thermodynamics that limit the extent of conversion to condensation products. The present invention has revealed that conducting the reaction with the condensation catalysts and at the temperatures and pressures described below overcomes these limitations and unexpectedly promotes an immediate conversion of the condensation products to hydrocarbons, ketones and alcohols. The conversion, in turn, removes the condensation products from the reaction, thereby overcoming the thermodynamic limitations of the system to allow additional condensation reactions to occur. Elevated temperature and/or pressure conditions also avoid excessive conversion of the oxygenates directly to their corresponding hydrocarbons. The process also has the added benefit of allowing for the condensation reactions, deoxygenation reactions and APR reactions to occur in a single reactor and under steady-state equilibrium.

For any given reaction, the free energy change is indicative of the favorability of the forward reaction. The more negative the free energy change, the more favorable the reaction. As a result, reactions associated with a highly negative change in free energy are generally favorable and have the potential to exhibit high conversions to reaction products. Conversely, reactions associated with positive changes in free energy are not favorable and are inherently limited in the extent to which reactants are converted to products. As an illustration, FIG. 4 shows the free energy changes associated with steps along the reaction pathway for converting acetone and hydrogen to a C₆ hydrocarbon (2-methylpentane) and water at 100° C. and 400° C. The known free energy levels of the stable intermediates derived along this pathway are shown with a solid line. The first step in the reaction pathway is the aldol condensation of two molecules of acetone to form one molecule of diacetone alcohol. The reaction at the lower temperature (100° C.) has a free energy change of −53 KJ/mole and is thermodynamically favored, while the reaction at the higher temperature (400° C.) is less favorable due to a free energy change of −10 KJ/mole. The implication is that the maximum conversion of pure acetone to diacetone alcohol for this step decreases as the temperature is increased (greater than 99% theoretical maximal conversion at 100° C. at atmospheric pressure, to only 15% at 400° C. at atmospheric pressure). Accordingly, the thermodynamic equilibrium limitation imposes an absolute limit to the amount of diacetone alcohol that may be produced under given conditions and in the absence of other reactions. This is further illustrated in FIG. 5, which provides the equilibrium constants associated with the intermediate reaction products and the overall conversion for the reaction of 2 moles of acetone with 3 moles of hydrogen to form 1 mole of 2-methylpentane and 2 moles of water. It can be seen that the equilibrium constant for the conversion of acetone to diacetone alcohol decreases with increasing temperature.

The present invention obviates this issue by immediately converting the condensation product to a compound that provides a more favorable reaction environment. In the case above, by removing the diacetone alcohol from the reaction mixture through a dehydration reaction that forms mesityl oxide, additional diacetone alcohol can be formed. In particular, the combination of a condensation and dehydration step to provide mesityl oxide and water from acetone provides a slightly more favorable reaction environment. As illustrated in FIG. 5, the conversion of acetone to mesityl oxide and water is slightly more favorable at the higher temperatures.

The total reaction system pressure also has a beneficial effect on the maximal theoretical extent to which reactant may form a product. Considering the condensation reaction example above, the conversion of acetone to diacetone alcohol is limited to 15% at 400° C. at atmospheric pressure with pure acetone feed. By increasing the system pressure to 600 psi gauge pressure, the equilibrium conversion shifts so that up to 76% conversion may be achieved at the same temperature. For reactions exhibiting a net decrease in the number of moles of product as compared to the moles of reactant, an increase in system pressure (with all other conditions held constant) will act to increase the equilibrium product conversion. For the overall conversion of ketones to hydrocarbons, there is typically a net decrease in the moles of product compared to the moles of reactant, thus higher reaction pressures would lead to higher potential equilibrium conversions.

The process of preparing the component derived from a water-soluble oxygenated hydrocarbon in the present invention strikes a balance with the above thermodynamic limitations by operating with condensation catalysts and at temperature and pressure conditions that offset any reduction in the production of condensation products with an increase in the conversion to other downstream products. The kinetics of the entire system is also more favorable such that products may be produced continuously and at a more desirable rate. In terms of scaled-up production, after start-up, the reactor systems may be process controlled, and the reactions could proceed at steady-state equilibrium.

Oxygenates

The C₄₊ compounds are derived from oxygenates. As used herein in relation to the process of preparing the component derived from a water-soluble oxygenated hydrocarbon, “oxygenates” generically refers to hydrocarbon compounds having 1 or more carbon atoms and between 1 and 3 oxygen atoms (referred to herein as C₁₊O₁₋₃ hydrocarbons), such as alcohols, ketones, aldehydes, furans, hydroxy carboxylic acids, carboxylic acids, diols and triols. Preferably, the oxygenates have from 1 to 6 carbon atoms, or 2 to 6 carbon atoms, or 3 to 6 carbon atoms. Alcohols may include, without limitation, primary, secondary, linear, branched or cyclic C₁₊ alcohols, such as methanol, ethanol, n-propyl alcohol, isopropyl alcohol, butyl alcohol, isobutyl alcohol, butanol, pentanol, cyclopentanol, hexanol, cyclohexanol, 2-methyl-cyclopentanonol, heptanol, octanol, nonanol, decanol, undecanol, dodecanol, and isomers thereof. The ketones may include, without limitation, hydroxyketones, cyclic ketones, diketones, acetone, propanone, 2-oxopropanal, butanone, butane-2,3-dione, 3-hydroxybutan-2-one, pentanone, cyclopentanone, pentane-2,3-dione, pentane-2,4-dione, hexanone, cyclohexanone, 2-methyl-cyclopentanone, heptanone, octanone, nonanone, decanone, undecanone, dodecanone, methylglyoxal, butanedione, pentanedione, diketohexane, and isomers thereof. The aldehydes may include, without limitation, hydroxyaldehydes, acetaldehyde, propionaldehyde, butyraldehyde, pentanal, hexanal, heptanal, octanal, nonal, decanal, undecanal, dodecanal, and isomers thereof. The carboxylic acids may include, without limitation, formic acid, acetic acid, propionic acid, butanoic acid, pentanoic acid, hexanoic acid, heptanoic acid, isomers and derivatives thereof, including hydroxylated derivatives, such as 2-hydroxybutanoic acid and lactic acid. The diols may include, without limitation, ethylene glycol, propylene glycol, 1,3-propanediol, butanediol, pentanediol, hexanediol, heptanediol, octanediol, nonanediol, decanediol, undecanediol, dodecanediol, and isomers thereof. The triols may include, without limitation, glycerol, 1,1,1 tris(hydroxymethyl)-ethane (trimethylolethane), trimethylolpropane, hexanetriol, and isomers thereof. Furans and furfurals include, without limitation, furan, tetrahydrofuran, dihydrofuran, 2-furan methanol, 2-methyl-tetrahydrofuran, 2,5-dimethyl-tetrahydrofuran, 2-methyl furan, 2-ethyl-tetrahydrofuran, 2-ethyl furan, hydroxylmethylfurfural, 3-hydroxytetrahydrofuran, tetrahydro-3-furanol, 2,5-dimethyl furan, 5-hydroxymethyl-2(5H)-furanone, dihydro-5-(hydroxymethyl)-2(3H)-furanone, tetrahydro-2-furoic acid, dihydro-5-(hydroxymethyl)-2(3H)-furanone, tetrahydrofurfuryl alcohol, 1-(2-furyl)ethanol, hydroxymethyltetrahydrofurfural, and isomers thereof.

The oxygenates may originate from any source, but are preferably derived from biomass. As used herein, the term “biomass” refers to, without limitation, organic materials produced by plants (such as leaves, roots, seeds and stalks), and microbial and animal metabolic wastes. Common sources of biomass include: (1) agricultural wastes, such as corn stalks, straw, seed hulls, sugarcane leavings, bagasse, nutshells, and manure from cattle, poultry, and hogs; (2) wood materials, such as wood or bark, sawdust, timber slash, and mill scrap; (3) municipal waste, such as waste paper and yard clippings; and (4) energy crops, such as poplars, willows, switch grass, alfalfa, prairie bluestream, corn, soybean, and the like. The term also refers to the primary building blocks of the above, namely, saccharides, lignin, cellulosics, hemicellulose and starches, among others.

Oxygenates from biomass may be produced by any known method. Such methods include fermentation technologies using enzymes or microorganisms, Fischer-Tropsch reactions to produce C₂₋₁₀ alpha alcohols, and pyrolysis technologies to produce alcohols from oil, among others. In one embodiment, the oxygenates are produced using catalytic reforming technologies, such as the BioForming™ technology developed by Virent Energy Systems, Inc. (Madison, Wis.).

Oxygenated Hydrocarbons

In one embodiment, the oxygenates are derived from the catalytic reforming of oxygenated hydrocarbons. The oxygenated hydrocarbons may be any water-soluble oxygenated hydrocarbon having one or more carbon atoms and at least one oxygen atom (referred to herein as C₁₊O₁₊ hydrocarbons). Preferably, the oxygenated hydrocarbon has 2 to 12 carbon atoms (C₁₋₁₂O₁₋₁₁ hydrocarbon), and more preferably 2 to 6 carbon atoms (C₁₋₆O₁₋₆ hydrocarbon). The oxygenated hydrocarbon may also have an oxygen-to-carbon ratio ranging from 0.5:1 to 1.5:1, including ratios of 0.75:1.0, 1.0:1.0, 1.25:1.0, 1.5:1.0, and other ratios between. In one example, the oxygenated hydrocarbon has an oxygen-to-carbon ratio of 1:1. Nonlimiting examples of preferred water-soluble oxygenated hydrocarbons include monosaccharides, disaccharides, polysaccharides, sugar, sugar alcohols, alditols, ethanediol, ethanedione, acetic acid, propanol, propanediol, propionic acid, glycerol, glyceraldehyde, dihydroxyacetone, lactic acid, pyruvic acid, malonic acid, butanediols, butanoic acid, aldotetroses, tautaric acid, aldopentoses, aldohexoses, ketotetroses, ketopentoses, ketohexoses, alditols, hemicelluloses, cellulosic derivatives, lignocellulosic derivatives, starches, polyols and the like. Preferably, the oxygenated hydrocarbon includes sugar, sugar alcohols, saccharides and other polyhydric alcohols. More preferably, the oxygenated hydrocarbon is a sugar, such as glucose, fructose, sucrose, maltose, lactose, mannose or xylose, or a sugar alcohol, such as arabitol, erythritol, glycerol, isomalt, lactitol, malitol, mannitol, sorbitol, xylitol, ribitol, or glycol.

Oxygenated hydrocarbons shall also refer to and include alcohols derived by hydrogenation or hydrogenolysis of any of the foregoing. In certain embodiments, it may be preferable to convert the starting oxygenated hydrocarbon to another oxygenated hydrocarbon form that can be more readily converted to the desired oxygenates (e.g., primary, secondary, tertiary or polyhydric alcohols). For instance, some sugars may not convert as efficiently to oxygenates as compared to their corresponding sugar alcohol derivatives. It may therefore be desirable to convert the starting material, such as a sugar, furfural, carboxylic acid, ketone, or furan, into its corresponding alcohol derivative, such as by hydrogenation, or to smaller alcohol molecules, such as by hydrogenolysis.

Various processes are known for hydrogenating sugars, furfurals, carboxylic acids, ketones, and furans to their corresponding alcohol form, including those disclosed by: B. S. Kwak et al. (WO2006/093364A1 and WO 2005/021475A1), involving the preparation of sugar alditols from monosaccharides by hydrogenation over a ruthenium catalyst; and Elliot et al. (U.S. Pat. Nos. 6,253,797 and 6,570,043), disclosing the use of a nickel and rhenium free ruthenium catalyst on a more than 75% rutile titania support to convert sugars to sugar alcohols, all incorporated herein by reference. Other suitable ruthenium catalysts are described by Arndt et al. in published U.S. patent application 2006/0009661 (filed Dec. 3, 2003), and Arena in U.S. Pat. No. 4,380,679 (filed Apr. 12, 1982), U.S. Pat. No. 4,380,680 (filed May 21, 1982), U.S. Pat. No. 4,503,274 (filed Aug. 8, 1983), U.S. Pat. No. 4,382,150 (filed Jan. 19, 1982), and U.S. Pat. No. 4,487,980 (filed Apr. 29, 1983), all incorporated herein by reference. The hydrogenation catalyst generally includes Cu, Re, Ni, Fe, Co, Ru, Pd, Rh, Pt, Os, Ir, and alloys or combinations thereof, either alone or with promoters such as W, Mo, Au, Ag, Cr, Zn, Mn, Sn, B, P, Bi, and alloys or combinations thereof. The hydrogenation catalyst may also include any one of the supports further described below, and depending on the desired functionality of the catalyst. Other effective hydrogenation catalyst materials include either supported nickel or ruthenium modified with rhenium. In general, the hydrogenation reaction is carried out at hydrogenation temperatures of between about 80° C. to 250° C., and hydrogenation pressures in the range of about 100 psig to 2000 psig. The hydrogen used in the reaction may include in situ generated H₂, external H₂, recycled H₂, or a combination thereof.

The hydrogenation catalyst may also include a supported Group VIII metal catalyst and a metal sponge material, such as a sponge nickel catalyst. Activated sponge nickel catalysts (e.g., Raney nickel) are a well-known class of materials effective for various hydrogenation reactions. One type of sponge nickel catalyst is the type A7063 catalyst available from Activated Metals and Chemicals, Inc., Sevierville, Tenn. The type A7063 catalyst is a molybdenum promoted catalyst, typically containing approximately 1.5% molybdenum and 85% nickel. The use of the sponge nickel catalyst with a feedstock comprising xylose and dextrose is described by M. L. Cunningham et al. in U.S. Pat. No. 6,498,248, filed Sep. 9, 1999, incorporated herein by reference. The use of a Raney nickel catalyst with hydrolyzed corn starch is also described in U.S. Pat. No. 4,694,113, filed Jun. 4, 1986, and incorporated herein by reference.

The preparation of suitable Raney nickel hydrogenation catalysts is described by A. Yoshino et al. in published U.S. patent application 2004/0143024, filed Nov. 7, 2003, incorporated herein by reference. The Raney nickel catalyst may be prepared by treating an alloy of approximately equal amounts by weight of nickel and aluminum with an aqueous alkali solution, e.g., containing about 25 wt. % of sodium hydroxide. The aluminum is selectively dissolved by the aqueous alkali solution leaving particles having a sponge construction and composed predominantly of nickel with a minor amount of aluminum. Promoter metals, such as molybdenum or chromium, may be also included in the initial alloy in an amount such that about 1-2 wt. % remains in the sponge nickel catalyst.

In another embodiment, the hydrogenation catalyst is prepared by impregnating a suitable support material with a solution of ruthenium (III) nitrosylnitrate, ruthenium (III) nitrosylnitrate, or ruthenium (III) chloride in water to form a solid that is then dried for 13 hours at 120° C. in a rotary ball oven (residual water content is less than 1% by weight). The solid is then reduced at atmospheric pressure in a hydrogen stream at 300° C. (uncalcined) or 400° C. (calcined) in the rotary ball furnace for 4 hours. After cooling and rendering inert with nitrogen, the catalyst may then be passivated by passing over 5% by volume of oxygen in nitrogen for a period of 120 minutes.

In yet another embodiment, the hydrogenation reaction is performed using a catalyst comprising a nickel-rhenium catalyst or a tungsten-modified nickel catalyst. One example of a suitable hydrogenation catalyst is the carbon-supported nickel-rhenium catalyst composition disclosed by Werpy et al. in U.S. Pat. No. 7,038,094, filed Sep. 30, 2003, and incorporated herein by reference.

In other embodiments, it may also be desirable to convert the starting oxygenated hydrocarbon, such as a sugar, sugar alcohol or other polyhydric alcohol, to a smaller molecule that can be more readily converted to the desired oxygenates, such as by hydrogenolysis. Such smaller molecules may include primary, secondary, tertiary or polyhydric alcohols having less carbon atoms than the originating oxygenated hydrocarbon. Various processes are known for such hydrogenolysis reactions, including those disclosed by: Werpy et al. in U.S. Pat. No. 6,479,713 (filed Oct. 23, 2001), U.S. Pat. No. 6,677,385 (filed Aug. 6, 2002), U.S. Pat. No. 6,6841,085 (filed Oct. 23, 2001) and U.S. Pat. No. 7,083,094 (filed Sep. 30, 2003), all incorporated herein by reference and describing the hydrogenolysis of 5 and 6 carbon sugars and sugar alcohols to propylene glycol, ethylene glycol and glycerol using a rhenium-containing multi-metallic catalyst. Other systems include those described by Arena in U.S. Pat. No. 4,401,823 (filed May 18, 1981) directed to the use of a carbonaceous pyropolymer catalyst containing transition metals (such as chromium, molybdenum, tungsten, rhenium, manganese, copper, cadmium) or Group VIII metals (such as iron, cobalt, nickel, platinum, palladium, rhodium, ruthenium, iridium and osmium) to produce alcohols, acids, ketones, and ethers from polyhydroxylated compounds, such as sugars and sugar alcohols, and U.S. Pat. No. 4,496,780 (filed Jun. 22, 1983) directed to the use of a catalyst system having a Group VIII noble metal on a solid support with an alkaline earth metal oxide to produce glycerol, ethylene glycol and 1,2-propanediol from carbohydrates, each incorporated herein by reference. Another system includes that described by Dubeck et al. in U.S. Pat. No. 4,476,331 (filed Sep. 6, 1983) directed to the use of a sulfide-modified ruthenium catalyst to produce ethylene glycol and propylene glycol from larger polyhydric alcohols, such as sorbitol, also incorporated herein by reference. Other systems include those described by Saxena et al., “Effect of Catalyst Constituents on (Ni, Mo and Cu)/Kieselguhr-Catalyzed Sucrose Hydrogenolysis,” Ind. Eng. Chem. Res. 44, 1466-1473 (2005), describing the use of Ni, W, and Cu on a kieselguhr support, incorporated herein by reference.

In one embodiment, the hydrogenolysis catalyst includes Cr, Mo, W, Re, Mn, Cu, Cd, Fe, Co, Ni, Pt, Pd, Rh, Ru, Ir, or Os, and alloys or combinations thereof, either alone or with promoters such as Au, Ag, Cr, Zn, Mn, Sn, Bi, B, O and alloys or combinations thereof. Other effective hydrogenolysis catalyst materials may include the above metals combined with an alkaline earth metal oxide or adhered to catalytically active support, such as kieselguhr, or any one of the supports further described below.

The process conditions for carrying out the hydrogenolysis reaction will vary depending on the type of feedstock and desired products. In general, the hydrogenolysis reaction is conducted at temperatures of at least 110° C., or between 110° C. and 300° C., or between 170° C. and 240° C. The reaction should also be conducted under basic conditions, preferably at a pH of about 8 to about 13, or at a pH of about 10 to about 12. The reaction should also be conducted at pressures of between about 10 psig and 2400 psig, or between about 250 psig and 2000 psig, or between about 700 psig and 1600 psig.

The hydrogen used in the reaction may include in situ generated H₂, external H₂, recycled H₂, or a combination thereof.

Production of Oxygenates

The oxygenates are prepared by reacting an aqueous feedstock solution containing water and the water soluble oxygenated hydrocarbons with hydrogen over a catalytic material to produce the desired oxygenates. Preferably, the hydrogen is generated in situ using aqueous phase reforming (in situ generated H₂ or APR H₂), or a combination of APR H₂, external H₂ or recycled H₂, or just simply external H₂ or recycled H₂. The term “external H₂” refers to hydrogen that does not originate from the feedstock solution, but is added to the reactor system from an external source. The term “recycled H₂” refers to unconsumed hydrogen that originates from the feedstock solution, and which is collected and then recycled back into the reactor system for further use. External H₂ and recycled H₂ may also be referred to collectively or individually as “supplemental H₂.” In general, supplemental H₂ may be added for purposes of supplementing the APR hydrogen, or to substitute the inclusion of an APR hydrogen production step, or to increase the reaction pressure within the system, or to increase the molar ratio of hydrogen to carbon and/or oxygen in order to enhance the production yield of certain reaction product types, such as ketones and alcohols.

In processes utilizing APR H₂, the oxygenates are prepared by catalytically reacting a portion of the aqueous feedstock solution containing water and the water soluble oxygenated hydrocarbons in the presence of an APR catalyst at a reforming temperature and reforming pressure to produce the APR H₂, and catalytically reacting the APR H₂ (and recycled H₂ and/or external H₂) with a portion of the feedstock solution in the presence of a deoxygenation catalyst at a deoxygenation temperature and deoxygenation pressure to produce the desired oxygenates. In systems utilizing recycled H₂ or external H₂ as a hydrogen source, the oxygenates are simply prepared by catalytically reacting the recycled H₂ and/or external H₂ with the feedstock solution in the presence of the deoxygenation catalyst at the deoxygenation temperatures and pressures. In each of the above, the oxygenates may also include recycled oxygenates (recycled C₁₊O₁₋₃ hydrocarbons). Unless otherwise indicated, any discussions of APR catalysts and deoxygenation catalysts are non-limiting examples of suitable catalytic materials.

The deoxygenation catalyst is preferably a heterogeneous catalyst having one or more materials capable of catalyzing a reaction between hydrogen and the oxygenated hydrocarbon to remove one or more of the oxygen atoms from the oxygenated hydrocarbon to produce alcohols, ketones, aldehydes, furans, carboxylic acids, hydroxy carboxylic acids, diols and triols. In general, the materials will be adhered to a support and may include, without limitation, Cu, Re, Fe, Ru, Ir, Co, Rh, Pt, Pd, Ni, W, Os, Mo, Ag, Au, alloys and combinations thereof. The deoxygenation catalyst may include these elements alone or in combination with one or more Mn, Cr, Mo, W, V, Nb, Ta, Ti, Zr, Y, La, Sc, Zn, Cd, Ag, Au, Sn, Ge, P, Al, Ga, In, Tl, and combinations thereof. In one embodiment, the deoxygenation catalyst includes Pt, Ru, Cu, Re, Co, Fe, Ni, W or Mo. In yet another embodiment, the deoxygenation catalyst includes Fe or Re and at least one transition metal selected from Ir, Ni, Pd, P, Rh, and Ru. In another embodiment, the catalyst includes Fe, Re and at least Cu or one Group VIIIB transition metal. The support may be any one of the supports further described below, including a nitride, carbon, silica, alumina, zirconia, titania, vanadia, ceria, zinc oxide, chromia, boron nitride, heteropolyacids, kieselguhr, hydroxyapatite, and mixtures thereof. The deoxygenation catalyst may also be atomically identical to the APR catalyst or the condensation catalyst.

The deoxygenation catalyst may also be a bi-functional catalyst. For example, acidic supports (e.g., supports having low isoelectric points) are able to catalyze dehydration reactions of oxygenated compounds, followed by hydrogenation reactions on metallic catalyst sites in the presence of H₂, again leading to carbon atoms that are not bonded to oxygen atoms. The bi-functional dehydration/hydrogenation pathway consumes H₂ and leads to the subsequent formation of various polyols, diols, ketones, aldehydes, alcohols and cyclic ethers, such as furans and pyrans. Catalyst examples include tungstated zirconia, titania zirconia, sulfated zirconia, acidic alumina, silica-alumina, zeolites and heteropolyacid supports. Heteropolyacids are a class of solid-phase acids exemplified by such species as H_(3+x)PMo_(12-x)V_(x)O₄₀, H₄SiW₁₂O₄₀, H₃PW₁₂O₄₀, and H₆P₂W₁₈O₆₂. Heteropolyacids are solid-phase acids having a well-defined local structure, the most common of which is the tungsten-based Keggin structure.

Loading of the first element (i.e., Cu, Re, Fe, Ru, Ir, Co, Rh, Pt, Pd, Ni, W, Os, Mo, Ag, Au, alloys and combinations thereof) is in the range of 0.25 wt % to 25 wt % on carbon, with weight percentages of 0.10% and 0.05% increments between, such as 1.00%, 1.10%, 1.15%, 2.00%, 2.50%, 5.00%, 10.00%, 12.50%, 15.00% and 20.00%. The preferred atomic ratio of the second element (i.e., Mn, Cr, Mo, W, V, Nb, Ta, Ti, Zr, Y, La, Sc, Zn, Cd, Ag, Au, Sn, Ge, P, Al, Ga, In, Tl, and combinations thereof) is in the range of 0.25-to-1 to 10-to-1, including any ratios between, such as 0.50, 1.00, 2.50, 5.00, and 7.50-to-1. If the catalyst is adhered to a support, the combination of the catalyst and the support is from 0.25 wt % to 10 wt % of the primary element.

To produce oxygenates, the oxygenated hydrocarbon is combined with water to provide an aqueous feedstock solution having a concentration effective for causing the formation of the desired reaction products. The water-to-carbon ratio on a molar basis is preferably from about 0.5:1 to about 100:1, including ratios such as 1:1, 2:1, 3:1, 4:1, 5:1, 6:1, 7:1, 8:1, 9:1, 10:1, 15:1, 25:1, 50:1 75:1, 100:1, and any ratios there-between. The feedstock solution may also be characterized as a solution having at least 1.0 weight percent (wt %) of the total solution as an oxygenated hydrocarbon. For instance, the solution may include one or more oxygenated hydrocarbons, with the total concentration of the oxygenated hydrocarbons in the solution being at least about 1%, 5%, 10%, 20%, 30%, 40%, 50%, 60%, 70%, 80% or greater by weight, including any percentages between, and depending on the oxygenated hydrocarbons used. In one embodiment, the feedstock solution includes at least about 10%, 20%, 30%, 40%, 50%, or 60% of a sugar, such as glucose, fructose, sucrose or xylose, or a sugar alcohol, such as sorbitol, mannitol, glycerol or xylitol, by weight. Water-to-carbon ratios and percentages outside of the above stated ranges are also included. Preferably the balance of the feedstock solution is water. In some embodiments, the feedstock solution consists essentially of water, one or more oxygenated hydrocarbons and, optionally, one or more feedstock modifiers described herein, such as alkali or hydroxides of alkali or alkali earth salts or acids. The feedstock solution may also include recycled oxygenated hydrocarbons recycled from the reactor system. The feedstock solution may also contain negligible amounts of hydrogen, preferably less than about 1.5 mole of hydrogen per mole of feedstock. In the preferred embodiments, hydrogen is not added to the feedstock solution.

The feedstock solution is reacted with hydrogen in the presence of the deoxygenation catalyst at deoxygenation temperature and pressure conditions, and weight hourly space velocity, effective to produce the desired oxygenates. The specific oxygenates produced will depend on various factors, including the feedstock solution, reaction temperature, reaction pressure, water concentration, hydrogen concentration, the reactivity of the catalyst, and the flow rate of the feedstock solution as it affects the space velocity (the mass/volume of reactant per unit of catalyst per unit of time), gas hourly space velocity (GHSV), and weight hourly space velocity (WHSV). For example, an increase in flow rate, and thereby a reduction of feedstock exposure to the catalysts over time, will limit the extent of the reactions which may occur, thereby causing increased yield for higher level diols and triols, with a reduction in ketone and alcohol yields.

The deoxygenation temperature and pressure are preferably selected to maintain at least a portion of the feedstock in the liquid phase at the reactor inlet. It is recognized, however, that temperature and pressure conditions may also be selected to more favorably produce the desired products in the vapor-phase. In general, the reaction should be conducted at process conditions wherein the thermodynamics of the proposed reaction are favorable. For instance, the minimum pressure required to maintain a portion of the feedstock in the liquid phase will likely vary with the reaction temperature. As temperatures increase, higher pressures will generally be required to maintain the feedstock in the liquid phase, if desired. Pressures above that required to maintain the feedstock in the liquid phase (i.e., vapor-phase) are also suitable operating conditions.

In condensed phase liquid reactions, the pressure within the reactor must be sufficient to maintain the reactants in the condensed liquid phase at the reactor inlet. For liquid phase reactions, the reaction temperature may be from about 80° C. to 300° C., and the reaction pressure from about 72 psig to 1300 psig. In one embodiment, the reaction temperature is between about 120° C. and 300° C., or between about 200° C. and 280° C., or between about 220° C. and 260° C., and the reaction pressure is preferably between about 72 and 1200 psig, or between about 145 and 1200 psig, or between about 200 and 725 psig, or between about 365 and 700 psig, or between about 600 and 650 psig.

For vapor phase reactions, the reaction should be carried out at a temperature where the vapor pressure of the oxygenated hydrocarbon is at least about 0.1 atm (and preferably a good deal higher), and the thermodynamics of the reaction are favorable. This temperature will vary depending upon the specific oxygenated hydrocarbon compound used, but is generally in the range of from about 100° C. to 600° C. for vapor phase reactions. Preferably, the reaction temperature is between about 120° C. and about 300° C., or between about 200° C. and about 280° C., or between about 220° C. and about 260° C.

In another embodiment, the deoxygenation temperature is between about 100° C. and 400° C., or between about 120° C. and 300° C., or between about 200° C. and 280° C., and the reaction pressure is preferably between about 72 and 1300 psig, or between about 72 and 1200 psig, or between about 200 and 725 psig, or between about 365 and 700 psig.

A condensed liquid phase method may also be performed using a modifier that increases the activity and/or stability of the catalyst system. It is preferred that the water and the oxygenated hydrocarbon are reacted at a suitable pH of from about 1.0 to about 10.0, including pH values in increments of 0.1 and 0.05 between, and more preferably at a pH of from about 4.0 to about 10.0. Generally, the modifier is added to the feedstock solution in an amount ranging from about 0.1% to about 10% by weight as compared to the total weight of the catalyst system used, although amounts outside this range are included within the present invention.

In general, the reaction should be conducted under conditions where the residence time of the feedstock solution over the catalyst is appropriate to generate the desired products. For example, the WHSV for the reaction may be at least about 0.1 gram of oxygenated hydrocarbon per gram of catalyst per hour, and more preferably the WHSV is about 0.1 to 40.0 g/g hr, including a WHSV of about 0.25, 0.5, 0.75, 1.0, 1.0, 1.1, 1.2, 1.3, 1.4, 1.5, 1.6, 1.7, 1.8, 1.9, 2.0, 2.1, 2.2, 2.3, 2.4, 2.5, 2.6, 2.7, 2.8, 2.9, 3.0, 3.1, 3.2, 3.3, 3.4, 3.5, 3.6, 3.7, 3.8, 3.9, 4.0, 4.1, 4.2, 4.3, 4.4, 4.5, 4.6, 4.7, 4.8, 4.9, 5.0, 6, 7, 8, 9, 10, 11, 12, 13, 14, 15, 20, 25, 30, 35, 40 g/g hr.

The hydrogen used in the deoxygenation reaction is preferably in-situ generated H₂, but may also be external or recycled H₂. When present, the amount of external H₂ is preferably provided sparingly. Most preferably, the amount of external H₂ is provided in amounts that provide less than one hydrogen atom per oxygen atom in all of the oxygenated hydrocarbons in the feedstock stream prior to contacting the deoxygenation catalyst. For example, the molar ratio between the external H₂ and the total water-soluble oxygenated hydrocarbons in the feedstock solution is preferably selected to provide no more than one hydrogen atom per oxygen atom in the oxygenated hydrocarbon. The molar ratio of the oxygenated hydrocarbons in the feedstock to the external H₂ introduced to the feedstock is also preferably not more than 1:1, or more preferably up to 2:1, 3:1, 5:1, 10:1, 20:1 or greater (including 4:1, 6:1, 7:1, 8:1, 9:1, 11:1, 12:1, 13:1, 14:1, 15:1, 16:1, 17:1, 18:1 and 19:1). The amount (moles) of external H₂ introduced to the feedstock is between 0-100%, 0-95%, 0-90%, 0-85%, 0-80%, 0-75%, 0-70%, 0-65%, 0-60%, 0-55%, 0-50%, 0-45%, 0-40%, 0-35%, 0-30%, 0-25%, 0-20%, 0-15%, 0-10%, 0-5%, 0-2%, or 0-1% of the total number of moles of the oxygenated hydrocarbon(s) in the feedstock, including all intervals between. When the feedstock solution, or any portion thereof, is reacted with APR hydrogen and external H₂, the molar ratio of APR hydrogen to external H₂ is at least 1:20; 1:15, 1:10, 1:5; 1:3, 1:2, 1:1, 2:1, 3:1, 5:1, 10:1, 15:1, 20:1, and ratios between (including 4:1, 6:1, 7:1, 8:1, 9:1, 11:1, 12:1, 13:1, 14:1, 15:1, 16:1, 17:1, 18:1 and 19:1, and vice-versa). Preferably, the oxygenated hydrocarbon is reacted with H₂ in the presence of an insignificantly effective amount of external H₂.

The amount of external H₂ (or supplemental H₂) added may be calculated by considering the concentration of the oxygenated hydrocarbons in the feedstock solution. Preferably, the amount of external H₂ added should provide a molar ratio of oxygen atoms in the oxygenated hydrocarbons to moles of hydrogen atoms (i.e., 2 oxygen atoms per molecule of H₂ gas) of less than or equal to 1.0. For example, where the feedstock is an aqueous solution consisting of glycerol (3 oxygen atoms), the amount of supplemental H₂ added to the feedstock is preferably not more than about 1.5 moles of H₂ per mole of glycerol (C₃H₈O₃), and preferably not more than about 1.25, 1.0, 0.75, 0.50 or 0.25. In general, the amount of supplemental H₂ added is less than 0.75-times, and more preferably not more than 0.67, 0.50, 0.33, 0.30, 0.25, 0.20, 0.15, 0.10, 0.05, 0.01-times the amount of total H₂ (APR H₂ and external H₂) that would provide a 1:1 atomic ratio of oxygen to hydrogen atoms.

The amount of APR H₂ within a reactor may be identified or detected by any suitable method. APR H₂ may be determined based on the composition of the product stream as a function of the composition of the feedstock stream, the catalyst composition(s) and the reaction conditions, independent of the actual reaction mechanism occurring within the feedstock stream. The amount of APR H₂ may be calculated based on the catalyst, reaction conditions (e.g., flow rate, temperature, pressure, etc.) and the contents of the feedstock and the reaction products. For example, the feedstock may be contacted with the APR catalyst (e.g., platinum) to generate APR H₂ in situ and a first reaction product stream in the absence of a deoxygenation catalyst. The feedstock may also be contacted with both the APR catalyst and the deoxygenation catalyst to produce a second reaction product stream. By comparing the composition of the first reaction product stream and the second reaction product stream at comparable reaction conditions, one may identify the presence of APR H₂ and calculate the amount of APR H₂ produced. For example, an increase in the amount of oxygenated compounds with greater degrees of hydrogenation in the reaction product compared to the feedstock components may indicate the presence of APR H₂.

In-Situ Hydrogen Production

One advantage of the process of preparing the component derived from a water-soluble oxygenated hydrocarbon in the present invention is that it allows for the production and use of in-situ generated H₂. The APR H₂ is produced from the feedstock under aqueous phase reforming conditions using an aqueous phase reforming catalyst (APR catalyst). The APR catalyst is preferably a heterogeneous catalyst capable of catalyzing the reaction of water and oxygenated hydrocarbons to form H₂ under the conditions described below. In one embodiment, the APR catalyst includes a support and at least one Group VIIIB metal, Fe, Ru, Os, Ir, Co, Rh, Pt, Pd, Ni, alloys and combinations thereof. The APR catalyst may also include at least one additional material from Group VIIIB, Group VIIB, Group VIB, Group VB, Group IVB, Group IIB, Group IB, Group IVA or Group VA metals, such as Cu, B, Mn, Re, Cr, Mo, Bi, W, V, Nb, Ta, Ti, Zr, Y, La, Sc, Zn, Cd, Ag, Au, Sn, Ge, P, Al, Ga, In, Tl, alloys and combinations thereof. The preferred Group VIIB metal includes Re, Mn, or combinations thereof. The preferred Group VIB metal includes Cr, Mo, W, or a combination thereof. The preferred Group VIIIB metals include Pt, Rh, Ru, Pd, Ni, or combinations thereof. The supports may include any one of the catalyst supports described below, depending on the desired activity of the catalyst system.

The APR catalyst may also be atomically identical to the deoxygenation catalyst or the condensation catalyst. For instance, the APR and deoxygenation catalyst may include Pt alloyed or admixed with Ni, Ru, Cu, Fe, Rh, Re, alloys and combinations thereof. The APR catalyst and deoxygenation catalyst may also include Ru alloyed or admixed with Ge, Bi, B, Ni, Sn, Cu, Fe, Rh, Pt, alloys and combinations thereof. The APR catalyst may also include Ni alloyed or admixed with Sn, Ge, Bi, B, Cu, Re, Ru, Fe, alloys and combinations thereof.

Preferred loading of the primary Group VIIIB metal is in the range of 0.25 wt % to 25 wt % on carbon, with weight percentages of 0.10% and 0.05% increments between, such as 1.00%, 1.10%, 1.15%, 2.00%, 2.50%, 5.00%, 10.00%, 12.50%, 15.00% and 20.00%. The preferred atomic ratio of the second material is in the range of 0.25-to-1 to 10-to-1, including ratios between, such as 0.50, 1.00, 2.50, 5.00, and 7.50-to-1.

A preferred catalyst composition is further achieved by the addition of oxides of Group IIIB, and associated rare earth oxides. In such event, the preferred components would be oxides of either lanthanum or cerium. The preferred atomic ratio of the Group IIIB compounds to the primary Group VIIIB metal is in the range of 0.25-to-1 to 10-to-1, including ratios between, such as 0.50, 1.00, 2.50, 5.00, and 7.50-to-1.

Another preferred catalyst composition is one containing platinum and rhenium. The preferred atomic ratio of Pt to Re is in the range of 0.25-to-1 to 10-to-1, including ratios there-between, such as 0.50, 1.00, 2.50, 5.00, and 7.00-to-1. The preferred loading of the Pt is in the range of 0.25 wt % to 5.0 wt %, with weight percentages of 0.10% and 0.05% between, such as 0.35%, 0.45%, 0.75%, 1.10%, 1.15%, 2.00%, 2.50%, 3.0%, and 4.0%.

Preferably, the APR catalyst and the deoxygenation catalyst are of the same atomic formulation. The catalysts may also be of different formulations. In such event, the preferred atomic ratio of the APR catalyst to the deoxygenation catalyst is in the range of 5:1 to 1:5, such as, without limitation, 4.5:1, 4.0:1, 3.5:1, 3.0:1, 2.5:1, 2.0:1, 1.5:1, 1:1, 1:1.5, 1:2.0, 1:2.5, 1:3.0, 1:3.5, 1:4.0, 1:4.5, and any amounts between.

Similar to the deoxygenation reactions, the temperature and pressure conditions are preferably selected to maintain at least a portion of the feedstock in the liquid phase at the reactor inlet. The reforming temperature and pressure conditions may also be selected to more favorably produce the desired products in the vapor-phase. In general, the APR reaction should be conducted at a temperature where the thermodynamics are favorable. For instance, the minimum pressure required to maintain a portion of the feedstock in the liquid phase will vary with the reaction temperature. As temperatures increase, higher pressures will generally be required to maintain the feedstock in the liquid phase. Any pressure above that required to maintain the feedstock in the liquid phase (i.e., vapor-phase) is also a suitable operating pressure. For vapor phase reactions, the reaction should be conducted at a reforming temperature where the vapor pressure of the oxygenated hydrocarbon compound is at least about 0.1 atm (and preferably a good deal higher), and the thermodynamics of the reaction are favorable. The temperature will vary depending upon the specific oxygenated hydrocarbon compound used, but is generally in the range of from about 100° C. to 450° C., or from about 100° C. to 300° C., for reactions taking place in the vapor phase. For liquid phase reactions, the reaction temperature may be from about 80° C. to 400° C., and the reaction pressure from about 72 psig to 1300 psig.

In one embodiment, the reaction temperature is between about 100° C. and 400° C., or between about 120° C. and 300° C., or between about 200° C. and 280° C., or between about 150° C. and 270° C. The reaction pressure is preferably between about 72 and 1300 psig, or between about 72 and 1200 psig, or between about 145 and 1200 psig, or between about 200 and 725 psig, or between about 365 and 700 psig, or between about 600 and 650 psig.

A condensed liquid phase method may also be performed using a modifier that increases the activity and/or stability of the APR catalyst system. It is preferred that the water and the oxygenated hydrocarbon are reacted at a suitable pH of from about 1.0 to 10.0, or at a pH of from about 4.0 to 10.0, including pH value increments of 0.1 and 0.05 between. Generally, the modifier is added to the feedstock solution in an amount ranging from about 0.1% to about 10% by weight as compared to the total weight of the catalyst system used, although amounts outside this range are included within the present invention.

Alkali or alkali earth salts may also be added to the feedstock solution to optimize the proportion of hydrogen in the reaction products. Examples of suitable water-soluble salts include one or more selected from the group consisting of an alkali or an alkali earth metal hydroxide, carbonate, nitrate, or chloride salt. For example, adding alkali (basic) salts to provide a pH of about pH 4.0 to about pH 10.0 can improve hydrogen selectivity of reforming reactions.

The addition of acidic compounds may also provide increased selectivity to the desired reaction products in the hydrogenation reactions described below. It is preferred that the water-soluble acid is selected from the group consisting of nitrate, phosphate, sulfate, chloride salts, and mixtures thereof. If an acidic modifier is used, it is preferred that it be present in an amount sufficient to lower the pH of the aqueous feed stream to a value between about pH 1.0 and about pH 4.0. Lowering the pH of a feed stream in this manner may increase the proportion of oxygenates in the final reaction products.

In general, the reaction should be conducted under conditions where the residence time of the feedstock solution over the APR catalyst is appropriate to generate an amount of APR hydrogen sufficient to react with a second portion of the feedstock solution over the deoxygenation catalyst to provide the desired oxygenates. For example, the WHSV for the reaction may be at least about 0.1 gram of oxygenated hydrocarbon per gram of APR catalyst, and preferably between about 1.0 to 40.0 grams of oxygenated hydrocarbon per gram of APR catalyst, and more preferably between about 0.5 to 8.0 grams of oxygenated hydrocarbon per gram of APR catalyst. In terms of scaled-up production, after start-up, the APR reactor system should be process controlled so that the reactions proceed at steady-state equilibrium.

Condensation Step

The oxygenates produced are then converted into C₄₊ compounds by condensation. Without being limited to any specific theories, it is believed that the acid condensation reactions generally consist of a series of steps involving: (a) the dehydration of oxygenates to olefins; (b) oligomerization of the olefins; (c) cracking reactions; (d) cyclization of larger olefins to form aromatics; (e) paraffin isomerization; and (f) hydrogen-transfer reactions to form paraffins. Basic condensation reactions are believed to generally consist of a series of steps involving: (1) aldol condensation to form a β-hydroxyketone or β-hydroxyaldehyde; (2) dehydration of the β-hydroxyketone or 3-hydroxyaldehyde to form a conjugated enone; (3) hydrogenation of the conjugated enone to form a ketone or aldehyde, which may participate in further condensation reactions or conversion to an alcohol or hydrocarbon; and (4) hydrogenation of carbonyls to alcohols, or vice-versa. Acid-base condensation reactions are believed to generally involve any of the previous acidic and/or basic reactions steps.

Production of the C₄₊ compounds occurs by condensation of the oxygenates in the presence of a condensation catalyst. The condensation catalyst will generally be a catalyst capable of forming longer chain compounds by linking two oxygen containing species through a new carbon-carbon bond, and converting the resulting compound to a hydrocarbon, alcohol or ketone, such as an acid catalyst, basic catalyst or a multi-functional catalyst having both acid and base functionality. The condensation catalyst may include, without limitation, carbides, nitrides, zirconia, alumina, silica, aluminosilicates, phosphates, zeolites, titanium oxides, zinc oxides, vanadium oxides, lanthanum oxides, yttrium oxides, scandium oxides, magnesium oxides, cerium oxides, barium oxides, calcium oxides, hydroxides, heteropolyacids, inorganic acids, acid modified resins, base modified resins, and combinations thereof. The condensation catalyst may include the above alone or in combination with a modifier, such as Ce, La, Y, Sc, P, B, Bi, Li, Na, K, Rb, Cs, Mg, Ca, Sr, Ba, and combinations thereof. The condensation catalyst may also include a metal, such as Cu, Ag, Au, Pt, Ni, Fe, Co, Ru, Zn, Cd, Ga, In, Rh, Pd, Ir, Re, Mn, Cr, Mo, W, Sn, Os, alloys and combinations thereof, to provide a metal functionality. The condensation catalyst may also be atomically identical to the APR catalyst and/or the deoxygenation catalyst.

The condensation catalyst may be self-supporting (i.e., the catalyst does not need another material to serve as a support), or may require a separate support suitable for suspending the catalyst in the reactant stream. One particularly beneficial support is silica, especially silica having a high surface area (greater than 100 square meters per gram), obtained by sol-gel synthesis, precipitation or fuming. In other embodiments, particularly when the condensation catalyst is a powder, the catalyst system may include a binder to assist in forming the catalyst into a desirable catalyst shape. Applicable forming processes include extrusion, pelletization, oil dropping, or other known processes. Zinc oxide, alumina, and a peptizing agent may also be mixed together and extruded to produce a formed material. After drying, this material is calcined at a temperature appropriate for formation of the catalytically active phase, which usually requires temperatures in excess of 450° C. Other catalyst supports may include those described in further detail below.

Acid Catalysts

The acid condensation reaction is performed using acidic catalysts. The acid catalysts may include, without limitation, aluminosilicates (zeolites), silica-alumina phosphates (SAPO), aluminum phosphates (ALPO), amorphous silica alumina, zirconia, sulfated zirconia, tungstated zirconia, tungsten carbide, molybdenum carbide, titania, acidic alumina, phosphated alumina, phosphated silica, sulfated carbons, phosphated carbons, acidic resins, heteropolyacids, inorganic acids, and combinations thereof. In one embodiment, the catalyst may also include a modifier, such as Ce, Y, Sc, La, P, B, Bi, Li, Na, K, Rb, Cs, Mg, Ca, Sr, Ba, and combinations thereof. The catalyst may also be modified by the addition of a metal, such as Cu, Ag, Au, Pt, Ni, Fe, Co, Ru, Zn, Cd, Ga, In, Rh, Pd, Ir, Re, Mn, Cr, Mo, W, Sn, Os, alloys and combinations thereof, to provide metal functionality, and/or sulfides and oxide of Ti, Zr, V, Nb, Ta, Mo, Cr, W, Mn, Re, Al, Ga, In, Fe, Co, Ir, Ni, Si, Cu, Zn, Sn, Cd, P, and combinations thereof. Gallium has also been found to be particularly useful as a promoter for the present process. The acid catalyst may be homogenous, self-supporting or adhered to any one of the supports further described below, including supports containing carbon, silica, alumina, zirconia, titania, vanadia, ceria, nitride, boron nitride, heteropolyacids, alloys and mixtures thereof.

Ga, In, Zn, Fe, Mo, Ag, Au, Ni, P, Sc, Y, Ta, and lanthanides may also be exchanged onto zeolites to provide a zeolite catalyst having activity. The term “zeolite” as used herein refers not only to microporous crystalline aluminosilicate but also for microporous crystalline metal-containing aluminosilicate structures, such as galloaluminosilicates and gallosilicates. Metal functionality may be provided by metals such as Cu, Ag, Au, Pt, Ni, Fe, Co, Ru, Zn, Cd, Ga, In, Rh, Pd, Ir, Re, Mn, Cr, Mo, W, Sn, Os, alloys and combinations thereof.

Examples of suitable zeolite catalysts include ZSM-5, ZSM-11, ZSM-12, ZSM-22, ZSM-23, ZSM-35 and ZSM-48. Zeolite ZSM-5, and the conventional preparation thereof, is described in U.S. Pat. Nos. 3,702,886; Re. 29,948 (highly siliceous ZSM-5); U.S. Pat. No. 4,100,262 and U.S. Pat. No. 4,139,600, all incorporated herein by reference. Zeolite ZSM-11, and the conventional preparation thereof, is described in U.S. Pat. No. 3,709,979, which is also incorporated herein by reference. Zeolite ZSM-12, and the conventional preparation thereof, is described in U.S. Pat. No. 3,832,449, incorporated herein by reference. Zeolite ZSM-23, and the conventional preparation thereof, is described in U.S. Pat. No. 4,076,842, incorporated herein by reference. Zeolite ZSM-35, and the conventional preparation thereof, is described in U.S. Pat. No. 4,016,245, incorporated herein by reference. Another preparation of ZSM-35 is described in U.S. Pat. No. 4,107,195, the disclosure of which is incorporated herein by reference. ZSM-48, and the conventional preparation thereof, is taught by U.S. Pat. No. 4,375,573, incorporated herein by reference. Other examples of zeolite catalysts are described in U.S. Pat. No. 5,019,663 and U.S. Pat. No. 7,022,888, also incorporated herein by reference.

As described in U.S. Pat. No. 7,022,888, the acid catalyst may be a bifunctional pentasil zeolite catalyst including at least one metallic element from the group of Cu, Ag, Au, Pt, Ni, Fe, Co, Ru, Zn, Cd, Ga, In, Rh, Pd, Ir, Re, Mn, Cr, Mo, W, Sn, Os, alloys and combinations thereof, or a modifier from the group of Ga, In, Zn, Fe, Mo, Au, Ag, Y, Sc, Ni, P, Ta, lanthanides, and combinations thereof. The zeolite preferably has a strong acidic and dehydrogenation sites, and may be used with reactant streams containing and an oxygenated hydrocarbon at a temperature of below 500° C. The bifunctional pentasil zeolite may have ZSM-5, ZSM-8 or ZSM-11 type crystal structure consisting of a large number of 5-membered oxygen-rings, i.e., pentasil rings. The zeolite with ZSM-5 type structure is a particularly preferred catalyst. The bifunctional pentasil zeolite catalyst is preferably Ga and/or In-modified ZSM-5 type zeolites such as Ga and/or In-impregnated H-ZSM-5, Ga and/or In-exchanged H-ZSM-5, H-gallosilicate of ZSM-5 type structure and H-galloaluminosilicate of ZSM-5 type structure. The bifunctional ZSM-5 type pentasil zeolite may contain tetrahedral aluminum and/or gallium present in the zeolite framework or lattice and octahedral gallium or indium. The octahedral sites are preferably not present in the zeolite framework but are present in the zeolite channels in a close vicinity of the zeolitic protonic acid sites, which are attributed to the presence of tetrahedral aluminum and gallium in the zeolite. The tetrahedral or framework Al and/or Ga is believed to be responsible for the acid function of zeolite and octahedral or non-framework Ga and/or In is believed to be responsible for the dehydrogenation function of the zeolite.

In one embodiment, the condensation catalyst may be a H-galloaluminosilicate of ZSM-5 type bifunctional pentasil zeolite having framework (tetrahedral) Si/Al and Si/Ga mole ratio of about 10-100 and 15-150, respectively, and non-framework (octahedral) Ga of about 0.5-5.0 wt. %. When these pentasil H-galloaluminosilicate zeolites are used as a condensation catalyst, the density of strong acid sites can be controlled by the framework Al/Si mole ratio: the higher the Al/Si ratio, the higher the density of strong acid sites. The highly dispersed non-framework gallium oxide species can be obtained by the degalliation of the zeolite by its pre-treatment with H₂ and steam. The zeolite containing strong acid sites with high density and also highly dispersed non-framework gallium oxide species in close proximity of the zeolite acid site is preferred. The catalyst may optionally contain any binder such as alumina, silica or clay material. The catalyst can be used in the form of pellets, extrudates and particles of different shapes and sizes.

The acidic catalysts may include one or more zeolite structures comprising cage-like structures of silica-alumina. Zeolites are crystalline microporous materials with well-defined pore structure. Zeolites contain active sites, usually acid sites, which can be generated in the zeolite framework. The strength and concentration of the active sites can be tailored for particular applications. Examples of suitable zeolites for condensing secondary alcohols and alkanes may comprise aluminosilicates optionally modified with cations, such as Ga, In, Zn, Mo, and mixtures of such cations, as described, for example, in U.S. Pat. No. 3,702,886, which is incorporated herein by reference. As recognized in the art, the structure of the particular zeolite or zeolites may be altered to provide different amounts of various hydrocarbon species in the product mixture. Depending on the structure of the zeolite catalyst, the product mixture may contain various amounts of aromatic and cyclic hydrocarbons.

Alternatively, solid acid catalysts such as alumina modified with phosphates, chloride, silica, and other acidic oxides could be used in practicing the present invention. Also, either sulfated zirconia or tungstated zirconia may provide the necessary acidity. Re and Pt/Re catalysts are also useful for promoting condensation of oxygenates to C₅₊ hydrocarbons and/or C₅₊ mono-oxygenates. The Re is sufficiently acidic to promote acid-catalyzed condensation. Acidity may also be added to activated carbon by the addition of either sulfates or phosphates.

Base Catalysts

The base condensation reaction is performed using a base catalyst. The base catalyst includes at least Li, Na, K, Cs, B, Rb, Mg, Ca, Sr, Si, Ba, Al, Zn, Ce, La, Y, Sc, Y, Zr, Ti, hydrotalcite, zinc-aluminate, phosphate, base-treated aluminosilicate zeolite, a basic resin, basic nitride, alloys or combinations thereof. The base catalyst may also include an oxide of Ti, Zr, V, Nb, Ta, Mo, Cr, W, Mn, Re, Al, Ga, In, Co, Ni, Si, Cu, Zn, Sn, Cd, Mg, P, Fe, and combinations thereof. In one embodiment, the condensation catalyst further includes a metal, such as Cu, Ag, Au, Pt, Ni, Fe, Co, Ru, Zn, Cd, Ga, In, Rh, Pd, Ir, Re, Mn, Cr, Mo, W, Sn, Os, alloys and combinations thereof. Preferred Group IA materials include Li, Na, K, Cs and Rb. Preferred Group IIA materials include Mg, Ca, Sr and Ba. Preferred Group IIB materials include Zn and Cd. Preferred Group IIIB materials include Y and La. Basic resins include resins that exhibit basic functionality, such as Amberlyst. The base catalyst may be self-supporting or adhered to any one of the supports further described below, including supports containing carbon, silica, alumina, zirconia, titania, vanadia, ceria, nitride, boron nitride, heteropolyacids, alloys and mixtures thereof.

The base catalyst may also include zeolites and other microporous supports that contain Group IA compounds, such as Li, Na, K, Cs and Rb. Preferably, the Group IA material is present in an amount greater than that required to neutralize the acidic nature of the support. These materials may be used in any combination, and also in combination with alumina or silica. A metal function may also be provided by the addition of group VIIIB metals, or Cu, Ga, In, Zn or Sn.

In one embodiment, the condensation catalyst is derived from the combination of MgO and Al₂O₃ to form a hydrotalcite material. Another preferred material contains ZnO and Al₂O₃ in the form of a zinc aluminate spinel. Yet another preferred material is a combination of ZnO, Al₂O₃, and CuO. Each of these materials may also contain an additional metal function provided by a Group VIIIB metal, such as Pd or Pt. In one embodiment, the base catalyst is a metal oxide containing Cu, Ni, Zn, V, Zr, or mixtures thereof. In another embodiment, the base catalyst is a zinc aluminate metal containing Pt, Pd Cu, Ni, or mixtures thereof.

Preferred loading of the primary metal is in the range of 0.10 wt % to 25 wt %, with weight percentages of 0.10% and 0.05% increments between, such as 1.00%, 1.10%, 1.15%, 2.00%, 2.50%, 5.00%, 10.00%, 12.50%, 15.00% and 20.00%. The preferred atomic ratio of the second metal, if any, is in the range of 0.25-to-1 to 10-to-1, including ratios there between, such as 0.50, 1.00, 2.50, 5.00, and 7.50-to-1.

Acid-Base Catalysts

The acid-base condensation reaction is performed using a multi-functional catalyst having both acid and base functionality. The acid-base catalyst may include hydrotalcite, zinc-aluminate, phosphate, Li, Na, K, Cs, B, Rb, Mg, Si, Ca, Sr, Ba, Al, Ce, La, Sc, Y, Zr, Ti, Zn, Cr, and combinations thereof. In further embodiments, the acid-base catalyst may also include one or more oxides from the group of Ti, Zr, V, Nb, Ta, Mo, Cr, W, Mn, Re, Al, Ga, In, Fe, Co, Ir, Ni, Si, Cu, Zn, Sn, Cd, P, and combinations thereof. The acid-base catalyst may also include a metal functionality provided by Cu, Ag, Au, Pt, Ni, Fe, Co, Ru, Zn, Cd, Ga, In, Rh, Pd, Ir, Re, Mn, Cr, Mo, W, Sn, Os, alloys or combinations thereof. In one embodiment, the catalyst further includes Zn, Cd or phosphate. In one embodiment, the condensation catalyst is a metal oxide containing Pd, Pt, Cu or Ni, and even more preferably an aluminate or zirconium metal oxide containing Mg and Cu, Pt, Pd or Ni. The acid-base catalyst may also include a hydroxyapatite (HAP) combined with any one or more of the above metals. The acid-base catalyst may be self-supporting or adhered to any one of the supports further described below, including supports containing carbon, silica, alumina, zirconia, titania, vanadia, ceria, nitride, boron nitride, heteropolyacids, alloys and mixtures thereof.

The condensation catalyst may also include zeolites and other microporous supports that contain Group IA compounds, such as Li, NA, K, Cs and Rb. Preferably, the Group IA material is present in an amount less than that required to neutralize the acidic nature of the support. A metal function may also be provided by the addition of group VIIIB metals, or Cu, Ga, In, Zn or Sn.

In one embodiment, the condensation catalyst is derived from the combination of MgO and Al₂O₃ to form a hydrotalcite material. Another preferred material contains a combination of MgO and ZrO₂, or a combination of ZnO and Al₂O₃. Each of these materials may also contain an additional metal function provided by copper or a Group VIIIB metal, such as Ni, Pd, Pt, or combinations of the foregoing.

If a Group IIB, VIB, VIIB, VIIIB, IIA or IVA metal is included, the loading of the metal is in the range of 0.10 wt % to 10 wt %, with weight percentages of 0.10% and 0.05% increments between, such as 1.00%, 1.10%, 1.15%, 2.00%, 2.50%, 5.00% and 7.50%, etc. If a second metal is included, the preferred atomic ratio of the second metal is in the range of 0.25-to-1 to 5-to-1, including ratios there between, such as 0.50, 1.00, 2.50 and 5.00-to-1.

Condensation Reactions

The specific C₄₊ compounds produced will depend on various factors, including, without limitation, the type of oxygenates in the reactant stream, condensation temperature, condensation pressure, the reactivity of the catalyst, and the flow rate of the reactant stream as it affects the space velocity, GHSV and WHSV. Preferably, the reactant stream is contacted with the condensation catalyst at a WHSV that is appropriate to produce the desired hydrocarbon products. The WHSV is preferably at least about 0.1 grams of oxygenate in the reactant stream per hour, more preferably the WHSV is between about 0.1 to 40.0 g/g hr, including a WHSV of about 1, 2, 3, 4, 5, 6, 7, 8, 9, 10, 11, 12, 13, 14, 15, 20, 25, 30, 35 g/g hr, and increments between.

In general, the condensation reaction should be carried out at a temperature at which the thermodynamics of the proposed reaction are favorable. For condensed phase liquid reactions, the pressure within the reactor must be sufficient to maintain at least a portion of the reactants in the condensed liquid phase at the reactor inlet. For vapor phase reactions, the reaction should be carried out at a temperature where the vapor pressure of the oxygenates is at least about 0.1 atm (and preferably a good deal higher), and the thermodynamics of the reaction are favorable. The condensation temperature will vary depending upon the specific oxygenate used, but is generally in the range of from about 80° C. to 500° C. for reactions taking place in the vapor phase, and more preferably from about 125° C. to 450° C. For liquid phase reactions, the condensation temperature may be from about 80° C. to 500° C., and the condensation pressure from about 0 psig to 1200 psig. Preferably, the condensation temperature is between about 125° C. and 300° C., or between about 125° C. and 250° C., or between about 250° C. and 425° C. The reaction pressure is preferably at least about 0.1 atm, or between about 0 and 1200 psig, or between about 0 and 1000 psig, or between about 0 and 700 psig.

Varying the factors above, as well as others, will generally result in a modification to the specific composition and yields of the C₄₊ compounds. For example, varying the temperature and/or pressure of the reactor system, or the particular catalyst formulations, may result in the production of C₄₊ alcohols and/or ketones instead of C₄₊ hydrocarbons. The C₄₊ hydrocarbon product may also contain a variety of olefins, and alkanes of various sizes (typically branched alkanes). Depending upon the condensation catalyst used, the hydrocarbon product may also include aromatic and cyclic hydrocarbon compounds. The C₄₊ hydrocarbon product may also contain undesirably high levels of olefins, which may lead to coking or deposits in combustion engines, or other undesirable hydrocarbon products. In such event, the hydrocarbon molecules produced may be optionally hydrogenated to reduce the ketones to alcohols and hydrocarbons, while the alcohols and unsaturated hydrocarbon may be reduced to alkanes, thereby forming a more desirable hydrocarbon product having low levels of olefins, aromatics or alcohols.

The finishing step will generally be a hydrogenation reaction that removes the remaining carbonyl group or hydroxyl group. In such event, any one of the hydrogenation catalysts described above may be used. Such catalysts may include any one or more of the following metals, Cu, Ni, Fe, Co, Ru, Pd, Rh, Pt, Ir, Os, alloys or combinations thereof, alone or with promoters such as Au, Ag, Cr, Zn, Mn, Sn, Cu, Bi, and alloys thereof, may be used in various loadings ranging from about 0.01 to about 20 wt % on a support as described above.

In general, the finishing step is carried out at finishing temperatures of between about 80° C. to 250° C., and finishing pressures in the range of about 100 psig to 2000 psig. The finishing step may be conducted in the vapor phase or liquid phase, and may use in situ generated H₂, external H₂, recycled H₂, or combinations thereof, as necessary.

Other factors, such as the concentration of water or undesired oxygenates, may also effect the composition and yields of the C₄₊ compounds, as well as the activity and stability of the condensation catalyst. In such event, the process may include a dewatering step that removes a portion of the water prior to condensation, or a separation unit for removal of the undesired oxygenates. For instance, a separator unit, such as a phase separator, extractor, purifier or distillation column, may be installed prior to the condensation step so as to remove a portion of the water from the reactant stream containing the oxygenates. A separation unit may also be installed to remove specific oxygenates to allow for the production of a desired product stream containing hydrocarbons within a particular carbon range, or for use as end products or in other systems or processes.

C₄₊ Compounds

The practice of the process of preparing the component derived from a water-soluble oxygenated hydrocarbon in the present invention results in the production of C₄₊ alkanes, C₄₊ alkenes, C₅₊ cycloalkanes, C₅₊ cycloalkenes, aryls, fused aryls, C₄₊ alcohols, C₄₊ ketones, and mixtures thereof. The C₄₊ alkanes and C₄₊ alkenes have from 4 to 30 carbon atoms (C₄₋₃₀ alkanes and C₄₋₃₀ alkenes) and may be branched or straight chained alkanes or alkenes. The C₄₊ alkanes and C₄₊ alkenes may also include fractions of C₄₋₉, C₇₋₁₄, C₁₂₋₂₄ alkanes and alkenes, respectively, with the C₄₋₉ fraction directed to gasoline, the C₇₋₁₄ fraction directed to kerosene (e.g. jet fuels), and the C₁₂₋₂₄ fraction directed to diesel fuel and other industrial applications. Examples of various C₄₊ alkanes and C₄₊ alkenes include, without limitation, butane, butane, pentane, pentene, 2-methylbutane, hexane, hexane, 2-methylpentane, 3-methylpentane, 2,2-dimethylbutane, 2,3-dimethylbutane, heptane, heptene, octane, octene, 2,2,4,-trimethylpentane, 2,3-dimethyl hexane, 2,3,4-trimethylpentane, 2,3-dimethylpentane, nonane, nonene, decane, decene, undecane, undecene, dodecane, dodecene, tridecane, tridecene, tetradecane, tetradecene, pentadecane, pentadecene, hexadecane, hexadecane, heptyldecane, heptyldecene, octyldecane, octyldecene, nonyldecane, nonyldecene, eicosane, eicosene, uneicosane, uneicosene, doeicosane, doeicosene, trieicosane, trieicosene, tetraeicosane, tetraeicosene, and isomers thereof.

The C₅₊ cycloalkanes and C₅₊ cycloalkenes have from 5 to 30 carbon atoms and may be unsubstituted, mono-substituted or multi-substituted. In the case of mono-substituted and multi-substituted compounds, the substituted group may include a branched C₃₊ alkyl, a straight chain C₁₊ alkyl, a branched C₃₊ alkylene, a straight chain C₁₊ alkylene, a straight chain C₂₊ alkylene, a phenyl or a combination thereof. In one embodiment, at least one of the substituted groups include a branched C₃₋₁₂ alkyl, a straight chain C₁₋₁₂ alkyl, a branched C₃₋₁₂ alkylene, a straight chain C₁₋₁₂ alkylene, a straight chain C₂₋₁₂ alkylene, a phenyl or a combination thereof. In yet another embodiment, at least one of the substituted groups include a branched C₃₋₄ alkyl, a straight chain C₁₋₄ alkyl, a branched C₃₋₄ alkylene, straight chain C₁₋₄ alkylene, straight chain C₂₋₄ alkylene, a phenyl or a combination thereof. Examples of desirable C₅₊ cycloalkanes and C₅₊ cycloalkenes include, without limitation, cyclopentane, cyclopentene, cyclohexane, cyclohexene, methyl-cyclopentane, methyl-cyclopentene, ethyl-cyclopentane, ethyl-cyclopentene, ethyl-cyclohexane, ethyl-cyclohexene, and isomers thereof.

Aryls will generally consist of an aromatic hydrocarbon in either an unsubstituted (phenyl), mono-substituted or multi-substituted form. In the case of mono-substituted and multi-substituted compounds, the substituted group may include a branched C₃₊ alkyl, a straight chain C₁₊ alkyl, a branched C₃₊ alkylene, a straight chain C₂₊ alkylene, a phenyl or a combination thereof. In one embodiment, at least one of the substituted groups include a branched C₃₋₁₂ alkyl, a straight chain C₁₋₁₂ alkyl, a branched C₃₋₁₂ alkylene, a straight chain C₂₋₁₂ alkylene, a phenyl or a combination thereof. In yet another embodiment, at least one of the substituted groups include a branched C₃₋₄ alkyl, a straight chain C₁₋₄ alkyl, a branched C₃₋₄ alkylene, straight chain C₂₋₄ alkylene, a phenyl or a combination thereof. Examples of various aryls include, without limitation, benzene, toluene, xylene (dimethylbenzene), ethyl benzene, para xylene, meta xylene, ortho xylene, C₉ aromatics.

Fused aryls will generally consist of bicyclic and polycyclic aromatic hydrocarbons, in either an unsubstituted, mono-substituted or multi-substituted form. In the case of mono-substituted and multi-substituted compounds, the substituted group may include a branched C₃₊ alkyl, a straight chain C₁₊ alkyl, a branched C₃₊ alkylene, a straight chain C₂₊ alkylene, a phenyl or a combination thereof. In another embodiment, at least one of the substituted groups include a branched C₃₋₄ alkyl, a straight chain C₁₋₄ alkyl, a branched C₃₋₄ alkylene, straight chain C₂₋₄ alkylene, a phenyl or a combination thereof. Examples of various fused aryls include, without limitation, naphthalene, anthracene, tetrahydronaphthalene, and decahydronaphthalene, indane, indene, and isomers thereof.

The C₄₊ alcohols may also be cyclic, branched or straight chained, and have from 4 to 30 carbon atoms. In general, the C₄₊ alcohols may be a compound according to the formula R¹—OH, wherein R¹ is a member selected from the group consisting of a branched C₄₊ alkyl, straight chain C₄₊ alkyl, a branched C₄₊ alkylene, a straight chain C₄₊ alkylene, a substituted C₅₊ cycloalkane, an unsubstituted C₅₊ cycloalkane, a substituted C₅+ cycloalkene, an unsubstituted C₅₊ cycloalkene, an aryl, a phenyl and combinations thereof. Examples of desirable C₄₊ alcohols include, without limitation, butanol, pentanol, hexanol, heptanol, octanol, nonanol, decanol, undecanol, dodecanol, tridecanol, tetradecanol, pentadecanol, hexadecanol, heptyldecanol, octyldecanol, nonyldecanol, eicosanol, uneicosanol, doeicosanol, trieicosanol, tetraeicosanol, and isomers thereof.

The C₄₊ ketones may also be cyclic, branched or straight chained, and have from 4 to 30 carbon atoms. In general, the C₄₊ ketone may be a compound according to the formula

wherein R³ and R⁴ are independently a member selected from the group consisting of a branched C₃₊ alkyl, a straight chain C₁₊ alkyl, a branched C₃₊ alkylene, a straight chain C₂₊ alkylene, a substituted C₅₊ cycloalkane, an unsubstituted C₅₊ cycloalkane, a substituted C₅₊ cycloalkene, an unsubstituted C₅₊ cycloalkene, an aryl, a phenyl and a combination thereof. Examples of desirable C₄₊ ketones include, without limitation, butanone, pentanone, hexanone, heptanone, octanone, nonanone, decanone, undecanone, dodecanone, tridecanone, tetradecanone, pentadecanone, hexadecanone, heptyldecanone, octyldecanone, nonyldecanone, eicosanone, uneicosanone, doeicosanone, trieicosanone, tetraeicosanone, and isomers thereof.

The lighter fractions of the above, primarily C₄-C₉, may be separated for gasoline use. Moderate fractions, such as C₇-C₁₄, may be separated for kerosene use (e.g. jet fuel), while heavier fractions, i.e., C₁₂-C₂₄, may be separated for diesel fuel use. The heaviest fractions may be used as lubricants or cracked to produce additional gasoline and/or diesel fractions.

Catalyst Supports

In various embodiments above, the catalyst systems include a support suitable for suspending the catalyst in the feedstock solution. The support should be one that provides a stable platform for the chosen catalyst and the reaction conditions. The support may take any form which is stable at the chosen reaction conditions to function at the desired levels, and specifically stable in aqueous feedstock solutions. Such supports include, without limitation, carbon, silica, silica-alumina, alumina, zirconia, titania, ceria, vanadia, nitride, boron nitride, heteropolyacids, hydroxyapatite, zinc oxide, chromia, and mixtures thereof. Nanoporous supports such as zeolites, carbon nanotubes, or carbon fullerene may also be used.

One particularly preferred catalyst support is carbon, especially carbon supports having relatively high surface areas (greater than 100 square meters per gram). Such carbons include activated carbon (granulated, powdered, or pelletized), activated carbon cloth, felts, or fibers, carbon nanotubes or nanohorns, carbon fullerene, high surface area carbon honeycombs, carbon foams (reticulated carbon foams), and carbon blocks. The carbon may be produced via either chemical or steam activation of peat, wood, lignite, coal, coconut shells, olive pits, and oil based carbon. Another preferred support is granulated activated carbon produced from coconuts. In one embodiment, the APR and deoxygenation catalyst system consists of Pt on carbon, with the Pt being further alloyed or admixed with Ni, Ru, Cu, Fe, Rh, Re, alloys and combinations thereof.

Another preferred catalyst support is zirconia. The zirconia may be produced via precipitation of zirconium hydroxide from zirconium salts, through sol-gel processing, or any other method. The zirconia is preferably present in a crystalline form achieved through calcination of the precursor material at temperatures exceeding 400° C. and may include both tetragonal and monoclinic crystalline phases. A modifying agent may be added to improve the textural or catalytic properties of the zirconia. Such modifying agents include, without limitation, sulfate, tungstenate, phosphate, titania, silica, and oxides of Group IIIB metals, especially Ce, La, or Y. In one embodiment, the APR and deoxygenation catalyst consists of Pt on a primarily tetragonal phase silica modified zirconia, with the Pt being further alloyed or admixed with Ni, Ru, Cu, Fe, Rh, Re, alloys and combinations thereof.

Yet another preferred catalyst support is titania. The titania may be produced via precipitation from titanium salts, through sol-gel processing, or any other method. The titania is preferably present in a crystalline form and may include both anatase and rutile crystalline phases. A modifying agent may be added to improve the textural or catalytic properties of the titania. Such modifying agents include, without limitation, sulfate, silica, and oxides of Group IIIB metals, especially Ce, La, or Y. In one embodiment, the APR and oxygenate forming catalyst system consists of Ru on a primarily rutile phase titania, with the Ru being further alloyed or admixed with Ge, Bi, B, Ni, Sn, Cu, Fe, Re, Rh, Pt, alloys and combinations thereof.

Another preferred catalyst support is silica. The silica may be optionally combined with alumina to form a silica-alumina material. In one embodiment, the APR catalyst system is Pt on silica-alumina or silica, with the Pt being further alloyed or admixed with Ni, Ru, Cu, Fe, Rh, Re, alloys and combinations thereof. In another embodiment, the APR catalyst system is Ni on silica-alumina or silica, with the nickel being further alloyed or admixed with Sn, Ge, Bi, Bu, Cu, Re, Ru, Fe, alloys and combinations thereof.

The support may also be treated or modified to enhance its properties. For example, the support may be treated, as by surface-modification, to modify surface moieties, such as hydrogen and hydroxyl. Surface hydrogen and hydroxyl groups can cause local pH variations that affect catalytic efficiency. The support may also be modified, for example, by treating it with sulfates, phosphates, tungstenates, silanes, lanthanides, alkali compounds or alkali earth compounds. For carbon supports, the carbon may be pretreated with steam, oxygen (from air), inorganic acids or hydrogen peroxide to provide more surface oxygen sites. The preferred pretreatment would be to use either oxygen or hydrogen peroxide. The pretreated carbon may also be modified by the addition of oxides of Group IVB and Group VB. It is preferred to use oxides of Ti, V, Zr and mixtures thereof.

The catalyst systems, whether alone or mixed together, may be prepared using conventional methods known to those in the art. Such methods include incipient wetting, evaporative impregnation, chemical vapor deposition, wash-coating, magnetron sputtering techniques, and the like. The method chosen to fabricate the catalyst is not particularly critical to the function of the invention, with the proviso that different catalysts will yield different results, depending upon considerations such as overall surface area, porosity, etc.

Supplemental Materials

Supplemental materials and compositions (“supplements”) may be added to the feedstock solution at various stages of the process in order to enhance the reaction or to drive it to the production of the desired reaction products. Supplements may include, without limitation, acids, salts and additional hydrogen or feedstock. Such supplements may be added directly to the feedstock stream prior to or contiguous with contacting the relevant catalyst, or directly to the reaction bed for the appropriate reactions.

In one embodiment, the supplement may include an additional feedstock solution for providing additional oxygenated hydrocarbons for oxygenate formation. The feedstock may include any one or more oxygenated hydrocarbons listed above, including any one or more sugar alcohols, glucose, polyols, glycerol or saccharides. For instance, the supplemental material may include glycerol. In this embodiment, crude glycerol is used to initiate the reaction and to produce hydrogen so as to avoid polluting the deoxygenation catalyst with contaminants from the crude glycerol. Purified glycerol is then added to the feedstock solution prior to or at the same time the original feedstock solution is placed in contact with the deoxygenation catalyst to increase the oxygenated hydrocarbons available for processing. It is anticipated that the opposite may be employed with the crude glycerol serving as the supplement depending on the characteristics of the APR catalyst and deoxygenation catalyst.

In another embodiment, the supplement may include additional oxygenates for the condensation reaction. The oxygenates may include any one or more oxygenates listed above. For instance, the supplemental material may include a propyl alcohol. In this embodiment, the propyl alcohol may be produced in a parallel system from a glycerol feedstock and then combined with oxygenates produced by the processing of a sorbitol feedstock in order to provide a reactant stream most effective to produce a product containing a combination of C₆₋₁₂ hydrocarbons.

In yet another embodiment, the supplemental material may include recycled oxygenates and/or oxygenated hydrocarbons not fully reacted during the production process. The oxygenates and oxygenated hydrocarbons may include any one or more of oxygenates and oxygenated hydrocarbons listed above.

In still yet another embodiment, the supplemental material may include acids and salts added to the process. The addition of acidic compounds may provide increased selectivity to the desired oxygenates and, ultimately, C₄₊ compounds. Water-soluble acids may include, without limitation, nitrate, phosphate, sulfate, chloride salts, and mixtures thereof. If an optional acidic modifier is used, it is preferred that it be present in an amount sufficient to lower the pH of the aqueous feed stream to a value between about pH 1.0 and about pH 4.0. Lowering the pH of a feed stream during oxygenate formation in this manner may increase the proportion of diols, polyols, ketones or alcohols for further condensation.

Reactor System

The reactions described herein may be carried out in any reactor of suitable design, including continuous-flow, batch, semi-batch or multi-system reactors, without limitation as to design, size, geometry, flow rates, etc. The reactor system may also use a fluidized catalytic bed system, a swing bed system, fixed bed system, a moving bed system, or a combination of the above. Preferably, the present invention is practiced utilizing a continuous-flow system at steady-state equilibrium.

In a continuous flow system, the reactor system includes at least a reforming bed adapted to receive an aqueous feedstock solution to produce hydrogen, a deoxygenation bed adapted to produce oxygenates from the hydrogen and a portion of the feedstock solution, and a condensation bed to produce C₄₊ compounds from the oxygenates. The reforming bed is configured to contact the aqueous feedstock solution in a vapor phase or liquid phase with the APR catalyst to provide hydrogen in a reactant stream. The deoxygenation bed is configured to receive the reactant stream for contact with the deoxygenation catalyst and production of the desired oxygenates. The condensation bed is configured to receive the reactant stream for contact with the condensation catalyst and production of the desired C₄₊ compounds. For systems not involving an APR hydrogen production step, the reforming bed may be removed. For systems not involving a hydrogen or oxygenate production step, the reforming and deoxygenation beds may be removed. Because the APR catalyst, deoxygenation catalyst and condensation catalyst may also be atomically identical, the catalysts may exist as the same bed. For systems with a hydrogenation or hydrogenolysis step, an additional reaction bed may be included prior to the deoxygenation and/or reforming bed. For systems with a finishing step, an additional reaction bed for conducting the finishing process may be included after the condensation bed.

In systems producing both hydrogen and oxygenates, the condensation bed may be positioned within the same reactor vessel along with the reforming bed or in a second reactor vessel in communication with a first reactor vessel having the reforming bed. The condensation bed may be within the same reactor vessel along with the reforming or deoxygenation bed or in a separate reactor vessel in communication with the reactor vessel having the deoxygenation bed. Each reactor vessel preferably includes an outlet adapted to remove the product stream from the reactor vessel. In systems including a hydrogenation step or hydrogenolysis step, the hydrogenation or hydrogenolysis reaction bed may be within the same reactor vessel along with the reforming or deoxygenation bed or in a separate reactor vessel in communication with the reactor vessel having the reforming bed and/or deoxygenation bed. For systems with a finishing step, the finishing reaction bed may be within the same reactor vessel along with the condensation bed or in a separate reactor vessel in communication with the reactor vessel having the condensation bed.

The reactor system may also include additional outlets to allow for the removal of portions of the reactant stream to further advance or direct the reaction to the desired reaction products, and to allow for the collection and recycling of reaction byproducts for use in other portions of the system. The reactor system may also include additional inlets to allow for the introduction of supplemental materials to further advance or direct the reaction to the desired reaction products, and to allow for the recycling of reaction byproducts for use in the reforming process. For example, the system may be designed such that excess hydrogen is produced over the APR catalyst, with a portion of the excess hydrogen removed and reintroduced downstream in the process to supplement the reaction of the oxygenates over the condensation catalyst or the finishing of the condensation product to arrive at the desired C₄₊ compounds. Alternatively, the system may be designed such that excess hydrogen is produced over the APR catalyst, with a portion of the excess hydrogen removed and used in other upstream processes, such as feedstock pretreatment processes and hydrogenation or hydrogenolysis reactions.

The reactor system may also include elements which allow for the separation of the reactant stream into different components which may find use in different reaction schemes or to simply promote the desired reactions. For instance, a separator unit, such as a phase separator, extractor, purifier or distillation column, may be installed prior to the condensation step to remove water from the reactant stream for purposes of advancing the condensation reaction to favor the production of hydrocarbons. A separation unit may also be installed to remove specific oxygenates to allow for the production of a desired product stream containing hydrocarbons within a particular carbon range, or for use as end products or in other systems or processes.

In one embodiment, the reaction system is configured such that the flow direction of the aqueous feedstock solution is established to ensure maximal interaction with the in-situ generated H₂. The reactor may be designed so that the reactant stream flows horizontally, vertical or diagonally to the gravitational plane so as to maximize the efficiency of the system. In systems where the reactant stream flows vertically or diagonally to the gravitational plan, the stream may flow either against gravity (up-flow system), with gravity (down-flow system), or a combination of both. In one preferred embodiment, the APR and/or deoxygenation reactor vessel is designed as an up-flow system while the condensation reactor vessel is designed as a down-flow system. In this embodiment, the feedstock solution first contacts a reforming bed containing the APR catalyst to produce in-situ generated H₂. Due to the configuration of the reactor, the APR H₂ is then able to, under certain conditions, percolate through a second reaction bed containing the deoxygenation catalyst at a rate greater than or equal to the feedstock solution to maximize the interaction of the feedstock solution with the H₂ and deoxygenation catalyst. The resulting reactant stream is then feed into the condensation reactor in a down-flow configuration for processing.

If the APR catalyst and deoxygenation catalyst are within a single chamber, the APR catalyst and deoxygenation catalyst may be placed in a stacked configuration to allow the feedstock solution to first contact the APR catalyst and then the deoxygenation catalyst, or a series of deoxygenation catalysts depending on the desired reaction products. The reaction beds for the APR catalyst and deoxygenation catalyst, or catalysts, may also be placed side-by-side dependent upon the particular flow mechanism employed. In either case, the feedstock solution may be introduced into the reaction vessel through one or more inlets, and then directed across the catalysts for processing. In another embodiment, the feedstock solution is directed across the APR catalyst to produce APR H₂, and then both the APR H₂ and the remaining feedstock solution are directed across the deoxygenation catalyst, or catalysts, to produce the desired oxygenates. In a parallel configuration, the feedstock solution may be separated to direct a first portion of the feedstock solution to the reforming bed where APR H₂ is produced, and a second portion to a deoxygenation bed where the desired oxygenates are produced using the in situ generated APR H₂. Alternatively, the reactor may be configured to accommodate the use of two separate feedstock solutions, with the first feedstock solution directed to the APR reactor vessel and the second feedstock solution directed to the deoxygenation reactor vessel. In a sequential configuration, the reactor may be designed so that the feedstock solution flows through the APR reactor vessel and into the deoxygenation reactor vessel. In embodiments employing a combined APR/deoxygenation catalyst, the generation of APR H₂ and oxygenates occurs simultaneously. In either of these systems, because the APR H₂ is produced in-situ, the pressure is provided by a pumping mechanism that also drives the feedstock solution through the reactor chambers.

FIG. 6 is a process diagram illustrating one potential reactor system useful in practicing the process of preparing the component derived from a water-soluble oxygenated hydrocarbon in the present invention. A feed stream of oxygenated hydrocarbons 1 (with or without water) is mixed with a stream of recycled water and recycled oxygenates at 2 to provide an aqueous feedstock solution 3. The feedstock solution 3 is then hydrogenated in a pretreatment step 4 to provide a feedstock solution 5 that is more readily converted to the desired oxygenates. The H₂ for the hydrogenation step may derive from an external source 22 or hydrogen recycled from the system as illustrated in steps 13-21 below. The feedstock solution 5 is reacted in a reactor vessel 8 that contains an APR catalyst and a deoxygenation catalyst to produce product stream 7 containing water, H₂, carbon dioxide, hydrocarbons and oxygenates. Water in product stream 7 is then removed at 8 to provide a product stream 10 containing oxygenates, hydrogen, carbon dioxide and hydrocarbons. Water from dewatering step 8 is then recycled at 9 and 15 for mixing with the stream of oxygenated hydrocarbons at 2. Product stream 10 is then passed through reactor vessel 11, which includes a condensation catalyst to produce product stream 12 containing C₄₊ compounds, water, H₂ and carbon dioxide. Product stream 12 is then passed through a three-phase separator 13 to separate the non-condensable gases 16 (i.e., hydrogen, carbon dioxide, methane, ethane, and propane) from the hydrocarbon product stream 14 containing C₄₊ compounds and water 15. Water 15 from the separator can be either recycled or exported from the system. The non-condensable gas stream 16 can be passed through a separation unit 17 to provide a purified H₂ stream 19 and a raffinate stream 18 containing carbon dioxide, methane, ethane, propane, and some hydrogen. The purified H₂ 19 may then be either exported from the system at 20 or passed through a recycle compressor 21 to provide recycled hydrogen stream 23.

In another preferred reactor system, illustrated in FIG. 7, a first reactor system is provided for converting the desired feedstock solution to C₄₊ compounds. The feedstock solution is stored in tank 1 and then passed through feed line 2 into charge pump 3. Charge pump 3 increases the pressure of the feedstock solution to the desired reaction pressure, e.g., 600 psi, and then discharges the solution through line 4 into an electric preheater 5 that heats the feed to the desired inlet temperature. The heated solution 6 is then passed into the process side of a reactor having essentially a tube-within-tube configuration (tube 7 within tube 8). Depending on the pressure of the reactor and the temperatures at which the several stages are operated, the reactant stream flowing through the reactor tube 7 will generally be maintained substantially in the liquid phase throughout, but may vaporize due to the heat of the condensation of the distal portion 7 b such that most of the product exiting the outlet end of the reactor through line 15 is in vapor form.

The stages and stage regions of the reactor tube 7 include an APR/deoxygenation catalyst (combined) and a condensation catalyst, each packed in successive catalytic beds (i.e., one on top of another). In this example, reactor tube 7 contains an APR/deoxygenation catalyst in the proximal portion 7 a of reactor tube 7 and a condensation catalyst at the distal portion 7 b. The catalyst system is supported at the bottom with small mesh stainless steel spheres setting on a stainless steel frit. Stainless steel spheres are also place on top of the catalyst bed. To facilitate separation of spent catalyst for recycling or regeneration, the catalyst beds are separated by means of a porous material, such as glass wool. The reactor may also be physically separated in separate tubes with conduits connecting the tubes to permit continuous flow. Such an arrangement may permit better thermal management, allowing optimization of temperature according to the requirements of the reactions in the several reactor stages.

The APR reaction is typically endothermic, while the condensation reaction is typically highly exothermic. Preferably, the reactor system permits the heat generated in the condensation reaction to be used to heat the APR and deoxygenation reactions. An advantage of conducting both of these reactions together is that heat is immediately transferred from the exothermic condensation reaction to the endothermic reforming/deoxygenation reactions.

The process tube 7 is preferably formed from a heat-conducting material configured to transfer heat from the distal portion 7 b to the proximal portion 7 a. In addition, the process tube may be heated with hot oil or hot air flowing through an annular space between process tube 7 and outer tube 8. The hot air may be generated by heating ambient air from a blower 10 with an electrical heater 12 and sent to the reactor through line 13. Hot oil may also be used and generated by a heater and pump (not shown) and sent to the reactor through line 13 as well. The flow configuration for this system is such that the hot air (or oil) in tube 8 flows countercurrent to the process fluid in tube 7. Accordingly, the reactor tube 7 is preferably warmer at the bottom than at the top.

Alternatively, the process tube 7 may be separated into two separate tubes or regions to facilitate the optimization of reaction conditions separately for the APR and deoxygenation reactions, and for the condensation reaction. For example, the separation of spent catalyst for regeneration may be simplified in this manner. In a two-region second stage in a vertical reactor, heat generated by condensation in the lower region may be permitted to move by convection to the upper region for use in the reformation reaction. The second region may also be configured to provide a continuous or step-wise gradient of mixed reformation and condensation catalysts, with more reformation catalyst at the upper end and more condensation catalyst at the lower end.

The effluent 15 from reactor tube 7 includes gaseous products (such as hydrogen, CO and CO₂) as well as aqueous and organic liquid products. The effluent is cooled to ambient temperature using a water cooled tube in a tube condenser 16. Effluent 17 from the condenser 16 is then directed to a three-phase separator to separate the product phases: the non-condensable gas 18 (upper phase), a lower density organic-liquid phase 19 (middle phase) and a higher-density aqueous-liquid phase 20 (lower phase). The system pressure is maintained by controlling the flow of non-condensable gas through line 21. The liquid level is maintained by controlling the flow of the aqueous-phase components through line 23. The organic-liquid phase is then skimmed off the top of the aqueous phase through line 22.

The aqueous phase 20 is withdrawn through line 23. If the aqueous phase 20 contains significant levels of residual oxygenates (i.e., products of incomplete reformation), the aqueous phase 20 may be conducted through line 23 back to feed source 6 where it is used for feedstock directed back into the reactor. In this way, the carbon content and energy value of the intermediate processes are recovered.

The middle phase 19 contains C₅₊ compounds. Typically, this phase contains hydrocarbons and mono-oxygenates ranging primarily from C₄ to C₃₀. Lighter fractions, primarily C₄-C₉, may be separated for gasoline use. The moderate fraction, i.e., C₇-C₁₄, may be separated for use as kerosene (e.g. in jet fuel). Heavier fractions, i.e., C₁₂-C₂₄, may be separated for diesel use. The heaviest fractions may be used as lubricants or cracked to produce additional gasoline and/or diesel fractions.

The vapor phase 18 contains hydrogen and other APR reaction products, such as carbon monoxide, carbon dioxide, methane, ethane, propane, butane, pentane, and/or hexane gas. Part of this gas is purged from the system to prevent the build-up of light hydrocarbons and CO₂ in the system through line 22. The gases may also be used as a fuel source for purposes of providing heat to the reactor system. In terms of scaled-up production, after start-up, the reactor systems could be process controlled, and the reactions would proceed at steady-state equilibrium.

Component Having at Least One C₄₊ Compound

The component having at least one C₄₊ compound derivable from a water-soluble oxygenated hydrocarbon by the process as described above is preferably separated into various distillation fractions by any known means before it is used in the liquid fuel compositions of the present invention. Preferably, the component having at least one C₄₊ compound derived from the process as described above is separated into more than one distillation fraction, wherein at least one of the distillation fractions is a lighter, moderate or heavier fraction described herein below.

As described above, the lighter fractions, primarily C₄-C₉, may be separated for gasoline use. The moderate fractions, e.g. C₇-C₁₄, may be separated for use as kerosene, e.g. for jet fuel use. Heavier fractions, e.g. C₁₂-C₂₄, may be separated for diesel fuel use. The heaviest fractions may be used as lubricants or may be cracked to produce additional fractions for use in gasoline, kerosene and/or diesel fractions.

Because the component having at least one C₄₊ compound derivable from a water-soluble oxygenated hydrocarbon is conveniently derived from biomass, the age of the component, or fractions thereof, is less than 100 years old, preferably less than 40 years old, more preferably less than 20 years old, as calculated from the carbon 14 concentration of the component.

Lighter Fractions

The lighter fractions of the component having at least one C₄₊ compound derivable from a water-soluble oxygenated hydrocarbon preferably has one or more of the following properties (LF-i to LF-vi):

-   (LF-i) a final boiling point in the range of from 150 to 220° C.,     more preferably in the range of from 160 to 210° C.; -   (LF-ii) a density at 15° C. in the range of from 700 to 890 kg/m³,     more preferably in the range of from 720 to 800 kg/m³; -   (LF-iii) a sulphur content of at most 5 mg/kg, more preferably at     most 1 mg/kg; -   (LF-iv) an oxygen content of at most 3.5% wt., more preferably at     most 3.0% wt., typically at most 2.7% wt.; -   (LF-v) a RON in the range of from 80 to 110, more preferably in the     range of from 90 to 100; -   (LF-vi) a MON in the range of from 70 to 100, more preferably in the     range of from 80 to 90.

Conveniently, the lighter fractions of the component having at least one C₄₊ compound derivable from a water-soluble oxygenated hydrocarbon has properties which accord with each of the properties detailed in LF-i to LF-vi above, more conveniently with each of the preferred values for each of the properties detailed in LF-i to LF-vi above.

Moderate Fractions

The moderate fractions of the component having at least one C₄₊ compound derivable from a water-soluble oxygenated hydrocarbon preferably has one or more of the following properties (MF-i to MF-vix):

-   (MF-i) an initial boiling point in the range of from 120 to 215° C.,     more preferably in the range of from 130 to 205° C.; -   (MF-ii) a final boiling point in the range of from 220 to 320° C.,     more preferably in the range of from 230 to 320° C.; -   (MF-iii) a density at 15° C. in the range of from 700 to 890 kg/m³,     more preferably in the range of from 730 to 840 kg/m³; -   (MF-iv) a sulphur content of at most 0.1% wt., more preferably at     most 0.01% wt.; -   (MF-v) a total aromatics content of at most 30% vol., more     preferably at most 25% vol., even more preferably at most 20% vol.,     most preferably at most 15% vol.; -   (MF-vi) a freeze point of −40° C. or lower, more preferably at least     −47° C. or lower; -   (MF-vii) a smoke point of at least 18 mm, more preferably at least     19 mm, even more preferably at least 25 mm; -   (MF-viii) a viscosity at −20° C. in the range of from 1 to 10 cSt,     more preferably in the range of from 2 to 8 cSt. -   (MF-vix) a specific energy content in the range of from 40 to 47     MJ/kg, more preferably in the range of from 42 to 46 MJ/kg.

Conveniently, the moderate fractions of the component having at least one C₄₊ compound derivable from a water-soluble oxygenated hydrocarbon has properties which accord with each of the properties detailed in MF-i to MF-vix above, more conveniently with each of the preferred values for each of the properties detailed in MF-i to MF-vix above.

Heavier Fractions

The heavier fractions of the component having at least one C₄₊ compound derivable from a water-soluble oxygenated hydrocarbon preferably has one or more of the following properties (HF-i to HF-vi):

-   (HF-i) a T95 in the range of from 220 to 380° C., more preferably in     the range of from 260 to 360° C.; -   (HF-ii) a flash point in the range of from 30 to 70° C., more     preferably in the range of from 33 to 60° C.; -   (HF-iii) a density at 15° C. in the range of from 700 to 900 kg/m³,     more preferably in the range of from 750 to 850 kg/m³; -   (HF-iv) a sulphur content of at most 5 mg/kg, more preferably at     most 1 mg/kg; -   (HF-v) an oxygen content of at most 10% wt., more preferably at most     8% wt.; -   (HF-vi) a viscosity at 40° C. in the range of from 0.5 to 6 cSt,     more preferably in the range of from 1 to 5 cSt.

Conveniently, the heavier fractions of the component having at least one C₄₊ compound derivable from a water-soluble oxygenated hydrocarbon has properties which accord with each of the properties detailed in HF-i to HF-vi above, more conveniently with each of the preferred values for each of the properties detailed in HF-i to HF-vi above.

Liquid Fuel Composition

The amount of the component having at least one C₄₊ compound derivable from a water-soluble oxygenated hydrocarbon present in the liquid fuel composition of the present invention is at least 0.1% vol., based on the overall volume of the liquid fuel composition. More preferably, the amount of the component derived from a water-soluble oxygenated hydrocarbon present in the liquid fuel composition of the present invention additionally accords with one or more of the parameters (i) to (xx) listed below:

(i) at least 0.5% vol. (ii) at least 1% vol (iii) at least 1.5% vol (iv) at least 2% vol (v) at least 2.5% vol (vi) at least 3% vol (vii) at least 3.5% vol (viii) at least 4% vol (ix) at least 4.5% vol (x) at least 5% vol (xi) at most 99.5% vol. (xii) at most 99% vol. (xiii) at most 98% vol. (xiv) at most 97% vol. (xv) at most 96% vol. (xvi) at most 95% vol. (xvii) at most 90% vol. (xviii) at most 85% vol. (xix) at most 80% vol. (xx) at most 75% vol.

Conveniently, the amount of the component having at least one C₄₊ compound derivable from a water-soluble oxygenated hydrocarbon present in the liquid fuel composition of the present invention accords with one parameter selected from (i) to (x) above, and one parameter selected from (xi) to (xx) above.

Conveniently, for gasoline compositions according to the present invention, the amount of the component having at least one C₄₊ compound derivable from a water-soluble oxygenated hydrocarbon present in the gasoline composition will be in the range of from 0.1 to 60% vol, 0.5 to 55% vol or 1 to 50% vol.

Conveniently, for diesel fuel compositions according to the present invention, the amount of the component having at least one C₄₊ compound derivable from a water-soluble oxygenated hydrocarbon present in the diesel fuel composition will be in the range of from 0.1 to 60% vol, 0.5 to 55% vol or 1 to 50% vol.

Conveniently, for kerosene compositions according to the present invention, the amount of the component having at least one C₄₊ compound derivable from a water-soluble oxygenated hydrocarbon present in the kerosene composition will be in the range of from 0.1 to 90% vol, 0.5 to 85% vol or 1 to 80% vol, such as in the range of from 0.1 to 60% vol, 0.5 to 55% vol or 1 to 50% vol.

The liquid fuel composition comprising of the present invention is typically selected from a gasoline, kerosene or diesel fuel composition.

If the liquid fuel composition is a gasoline composition, then the gasoline composition has an initial boiling point in the range of from 15° C. to 70° C. (IP123), a final boiling point of at most 230° C. (IP123), a RON in the range of from 85 to 110 (ASTM D2699) and a MON in the range of from 75 to 100 (ASTM D2700).

If the liquid fuel composition is a kerosene composition, then the kerosene composition has an initial boiling point in the range of from 110 to 150° C., a final boiling point in the range of from 200 to 320° C. and a viscosity at −20° C. in the range of from 0.8 to 10 mm²/s (ASTM D445).

If the liquid fuel composition is a diesel fuel composition, then the diesel fuel composition has an initial boiling point in the range of from 130° C. to 230° C. (IP123), a final boiling point of at most 410° C. (IP123) and a cetane number in the range of from 35 to 120 (ASTM D613).

Preferably, the liquid fuel composition of the present invention additionally comprises one or more fuel additive.

Gasoline Compositions

The gasoline composition according to the present invention typically comprise mixtures of hydrocarbons boiling in the range from 15 to 230° C., more typically in the range of from 25 to 230° C. (EN-ISO 3405). The initial boiling point of the gasoline compositions according to the present invention are in the range of from 15 to 70° C. (IP123), preferably in the range of from 20 to 60° C., more preferably in the range of from 25 to 50° C. The final boiling point of the gasoline compositions according to the present invention is at most 230° C., preferably at most 220° C., more preferably at most 210° C. The optimal ranges and distillation curves typically varying according to climate and season of the year.

In addition to the component having at least one C₄₊ compound derivable from a water-soluble oxygenated hydrocarbon, the hydrocarbons in the gasoline composition may be derived by any means known in the art, conveniently the hydrocarbons may be derived in any known manner from straight-run gasoline, synthetically-produced aromatic hydrocarbon mixtures, thermally or catalytically cracked hydrocarbons, hydro-cracked petroleum fractions, catalytically reformed hydrocarbons or mixtures of these.

The research octane number (RON) of the gasoline compositions according to the present invention is in the range of from 85 to 110 (ASTM D2699). Preferably, the RON of the gasoline composition will be at least 90, for instance in the range of from 90 to 110, more preferably at least 91, for instance in the range of from 91 to 105, even more preferably at least 92, for instance in the range of from 92 to 103, even more preferably at least 93, for instance in the range of from 93 to 102, and most preferably at least 94, for instance in the range of from 94 to 100.

The motor octane number (MON) of the gasoline compositions according to the present invention is in the range of from 75 to 100 (ASTM D2699). Preferably, the MON of the gasoline composition will be at least 80, for instance in the range of from 80 to 100, more preferably at least 81, for instance in the range of from 81 to 95, even more preferably at least 82, for instance in the range of from 82 to 93, even more preferably at least 83, for instance in the range of from 83 to 92, and most preferably at least 84, for instance in the range of from 84 to 90.

Typically, gasoline compositions comprise a mixture of components selected from one or more of the following groups; saturated hydrocarbons, olefinic hydrocarbons, aromatic hydrocarbons, and oxygenated hydrocarbons. Conveniently, the gasoline composition may comprise a mixture of saturated hydrocarbons, olefinic hydrocarbons, aromatic hydrocarbons, and, optionally, oxygenated hydrocarbons.

Typically, the olefinic hydrocarbon content of the gasoline composition is in the range of from 0 to 40 percent by volume based on the gasoline (ASTM D1319); preferably, the olefinic hydrocarbon content of the gasoline composition is in the range of from 0 to 30 percent by volume based on the gasoline composition, more preferably, the olefinic hydrocarbon content of the gasoline composition is in the range of from 0 to 20 percent by volume based on the gasoline composition.

Typically, the aromatic hydrocarbon content of the gasoline composition is in the range of from 0 to 70 percent by volume based on the gasoline (ASTM D1319), for instance the aromatic hydrocarbon content of the gasoline composition is in the range of from 10 to 60 percent by volume based on the gasoline composition; preferably, the aromatic hydrocarbon content of the gasoline composition is in the range of from 0 to 50 percent by volume based on the gasoline composition, for instance the aromatic hydrocarbon content of the gasoline composition is in the range of from 10 to 50 percent by volume based on the gasoline composition.

The benzene content of the gasoline composition is at most 10 percent by volume, more preferably at most 5 percent by volume, especially at most 1 percent by volume based on the gasoline composition.

The gasoline composition preferably has a low or ultra low sulphur content, for instance at most 1000 ppmw (parts per million by weight), preferably no more than 500 ppmw, more preferably no more than 100, even more preferably no more than 50 and most preferably no more than even 10 ppmw.

The gasoline composition also preferably has a low total lead content, such as at most 0.005 g/l, most preferably being lead free—having no lead compounds added thereto (i.e. unleaded).

When the gasoline composition comprises oxygenated hydrocarbons, at least a portion of non-oxygenated hydrocarbons will be substituted for oxygenated hydrocarbons. The oxygen content of the gasoline may be up to 30 percent by weight (EN 1601) based on the gasoline composition. For example, the oxygen content of the gasoline may be up to 25 percent by weight, preferably up to 10 percent by weight. Conveniently, the oxygenate concentration will have a minimum concentration selected from any one of 0, 0.2, 0.4, 0.6, 0.8, 1.0, and 1.2 percent by weight, and a maximum concentration selected from any one of 5, 4.5, 4.0, 3.5, 3.0, and 2.7 percent by weight.

Examples of oxygenated hydrocarbons, other than the oxygenated hydrocarbons that may be present in the component having at least one C₄₊ compound derivable from a water-soluble oxygenated hydrocarbon, that may be incorporated into the gasoline include alcohols, ethers, esters, ketones, aldehydes, carboxylic acids and their derivatives, and oxygen containing heterocyclic compounds. Preferably, the oxygenated hydrocarbons that may be incorporated into the gasoline are selected from alcohols (such as methanol, ethanol, propanol, iso-propanol, butanol, tert-butanol and iso-butanol), ethers (preferably ethers containing 5 or more carbon atoms per molecule, e.g., methyl tert-butyl ether) and esters (preferably esters containing 5 or more carbon atoms per molecule); a particularly preferred oxygenated hydrocarbon is ethanol.

When oxygenated hydrocarbons are present in the gasoline composition, the amount of oxygenated hydrocarbons in the gasoline composition may vary over a wide range. For example, gasolines comprising a major proportion of oxygenated hydrocarbons are currently commercially available in countries such as Brazil and U.S.A, e.g. E85, as well as gasolines comprising a minor proportion of oxygenated hydrocarbons, e.g. E10 and E5. Therefore, the amount of oxygenated hydrocarbons present in the gasoline composition is preferably selected from one of the following amounts: up to 85 percent by volume; up to 65 percent by volume; up to 30 percent by volume; up to 20 percent by volume; up to 15 percent by volume; and, up to 10 percent by volume, depending upon the desired final formulation of the gasoline. Conveniently, the gasoline composition may contain at least 0.5, 1.0 or 2.0 percent by volume oxygenated hydrocarbons.

Examples of suitable gasoline compositions include gasolines which have an olefinic hydrocarbon content of from 0 to 20 percent by volume (ASTM D1319), an oxygen content of from 0 to 5 percent by weight (EN 1601), an aromatic hydrocarbon content of from 0 to 50 percent by volume (ASTM D1319) and a benzene content of at most 1 percent by volume.

Whilst not critical to the present invention, the gasoline compositions of the present invention may conveniently additionally include one or more fuel additive. The concentration and nature of the fuel additive(s) that may be included in the gasoline composition of the present invention is not critical. Non-limiting examples of suitable types of fuel additives that can be included in the gasoline composition of the present invention include anti-oxidants, corrosion inhibitors, detergents, dehazers, antiknock additives, metal deactivators, valve-seat recession protectant compounds, dyes, friction modifiers, carrier fluids, diluents and markers. Examples of suitable such additives are described generally in U.S. Pat. No. 5,855,629.

Conveniently, the fuel additives can be blended with one or more diluents or carrier fluids, to form an additive concentrate, the additive concentrate can then be admixed with the gasoline composition of the present invention.

The (active matter) concentration of any additives present in the gasoline composition of the present invention is preferably up to 1 percent by weight, more preferably in the range from 5 to 1000 ppmw, advantageously in the range of from 75 to 300 ppmw, such as from 95 to 150 ppmw.

Alternatively, the gasoline composition of the present invention may be an aviation gasoline. If the gasoline composition is an aviation gasoline then, depending upon the grade of the aviation gasoline, the Lean Mixture Motor Octane Number will be at least 80 (ASTM D2700) and the Rich Mixture Octane Number will be at least 87 (ASTM D 909), or the Lean Mixture Motor Octane Number will be at least 99.5 (ASTM D2700) and the Performance Number will be at least 130 (ASTM D 909). Furthermore, if the gasoline composition is an aviation gasoline then the Reid Vapour Pressure at 37.8° C. will be in the range of from 38.0 to 49.0 kPa (ASTM D323), the final boiling point will be at most 170° C. (ASTM D 86), and the tetraethyl lead content will be at most 0.85 gPb/l.

Kerosene Fuel Compositions

The kerosene fuel compositions of the present invention have use in aviation engines, such as jet engines or aero diesel engines, but also in any other suitable power or lighting source.

In addition to the component having at least one C₄₊ compound derivable from a water-soluble oxygenated hydrocarbon, the kerosene fuel composition may comprise a mixture of two or more different fuel components, and/or be additivated as described below.

The kerosene fuel compositions will typically have boiling points within the range of 80 to 320° C., preferably in the range of 110 to 320° C., more preferably in the range of from 130 to 300° C., depending on grade and use. They will typically have a density from 775 to 845 kg/m³, preferably from 780 to 830 kg/m³, at 15° C. (e.g. ASTM D4502 or IP 365). They will typically have an initial boiling point in the range 80 to 150° C., preferably in the range 110 to 150° C., and a final boiling point in the range 200 to 320° C. Their kinematic viscosity at −20° C. (ASTM D445) is typically in the range of from 0.8 to 10 mm²/s, preferably from 1.2 to 8.0 mm²/s.

It may be desirable for the kerosene fuel composition to contain a Fischer-Tropsch derived fuel, if the kerosene fuel composition does contain a Fischer-Tropsch derived fuel, then it will conveniently contain 5% v or greater, preferably 10% v or greater, or more preferably 25% v or greater, of a Fischer-Tropsch derived fuel.

The Fischer-Tropsch derived fuel should be suitable for use as a kerosene fuel. Its components (or the majority, for instance 95% w or greater, thereof) should therefore have boiling points within the range given above, i.e. from 110 to 320° C., preferably from 130 to 300° C. It will suitably have a 90% v/v distillation temperature (T90) of from 180 to 250° C., preferably 180 to 230° C.

By “Fischer-Tropsch derived” is meant that the fuel is, or derives from, a synthesis product of a Fischer-Tropsch condensation process. The Fischer-Tropsch reaction converts carbon monoxide and hydrogen into longer chain, usually paraffinic, hydrocarbons:

n(CO+2H₂)=(—CH₂—)_(n) +nH₂O+heat,

in the presence of an appropriate catalyst and typically at elevated temperatures (e.g. 125 to 300° C., preferably 175 to 250° C.) and/or pressures (e.g. 500 to 10000 kPa, preferably 1200 to 5000 kPa). Hydrogen:carbon monoxide ratios other than 2:1 may be used if desired.

The carbon monoxide and hydrogen may themselves be derived from organic or inorganic, natural or synthetic sources, typically either from natural gas or from organically derived methane.

A kerosene product may be obtained directly from this reaction, or indirectly for instance by fractionation of a Fischer-Tropsch synthesis product or from a hydrotreated Fischer-Tropsch synthesis product. Hydrotreatment can involve hydrocracking to adjust the boiling range (see, e.g. GB-B-2077289 and EP-A-0147873) and/or hydroisomerisation which can improve base fuel cold flow properties by increasing the proportion of branched paraffins. EP-A-0583836 describes a two-step hydrotreatment process in which a Fischer-Tropsch synthesis product is firstly subjected to hydroconversion under conditions such that it undergoes substantially no isomerisation or hydrocracking (this hydrogenates the olefinic and oxygen-containing components), and then at least part of the resultant product is hydroconverted under conditions such that hydrocracking and isomerisation occur to yield a substantially paraffinic hydrocarbon fuel. The desired kerosene fraction(s) may subsequently be isolated for instance by distillation.

Other post-synthesis treatments, such as polymerisation, alkylation, distillation, cracking-decarboxylation, isomerisation and hydroreforming, may be used to modify the properties of Fischer-Tropsch condensation products, as described for example in U.S. Pat. No. 4,125,566 and U.S. Pat. No. 4,478,955.

Typical catalysts for the Fischer-Tropsch synthesis of paraffinic hydrocarbons comprise, as the catalytically active component, a metal from Group VIII of the periodic table, in particular ruthenium, iron, cobalt or nickel. Suitable such catalysts are described for example in EP-A-0583836 (pages 3 and 4).

An example of a Fischer-Tropsch based process is the SMDS (Shell Middle Distillate Synthesis) described in “The Shell Middle Distillate Synthesis Process”, van der Burgt et al (paper delivered at the 5^(th) Synfuels Worldwide Symposium, Washington D.C., November 1985; see also the November 1989 publication of the same title from Shell International Petroleum Company Ltd., London, UK). This process (also sometimes referred to as the Shell™ “Gas-to-Liquids” or “GTL” technology) produces middle distillate range products by conversion of a natural gas (primarily methane) derived synthesis gas into a heavy long-chain hydrocarbon (paraffin) wax which can then be hydroconverted and fractionated to produce liquid transport fuels such as kerosene fuel compositions. A version of the SMDS process, using a fixed-bed reactor for the catalytic conversion step, is currently in use in Bintulu, Malaysia and its products have been blended with petroleum derived gas oils in commercially available automotive fuels.

Gas oils and kerosenes prepared by the SMDS process are commercially available from the Royal Dutch/Shell Group of Companies.

Suitably, in accordance with the present invention, the Fischer-Tropsch derived kerosene fuel will consist of at least 90% w, preferably at least 95% w, more preferably at least 98% w, even more preferably at least 99% w, most preferably at least 99.8% w, of paraffinic components, typically normal and iso-paraffins. The weight ratio of normal to iso-paraffins will preferably be in the ranges indicated above. The actual value for this ratio will be determined, in part, by the hydroconversion process used to prepare the kerosene from the Fischer-Tropsch synthesis product. Some cyclic paraffins may also be present.

By virtue of the Fischer-Tropsch process, a Fischer-Tropsch derived kerosene has essentially no, or undetectable levels of, sulphur and nitrogen. Compounds containing these heteroatoms tend to act as poisons for Fischer-Tropsch catalysts and are therefore removed from the synthesis gas feed. Further, the process as usually operated produces no or virtually no aromatic components. The aromatics content of a Fischer-Tropsch kerosene, as determined by ASTM D4629, will typically be below 5% w, preferably below 2% w, more preferably below 1% w and most preferably below 0.2% w.

The Fischer-Tropsch derived kerosene which may be used in the kerosene fuel compositions of the present invention will typically have a density from 730 to 770 kg/m³ at 15° C.; a kinematic viscosity from 1.2 to 6, preferably from 2 to 5, more preferably from 2 to 3.5, mm²/s at −20° C.; and a sulphur content of 20 ppmw (parts per million by weight) or less, preferably of 5 ppmw or less.

Preferably it is a product prepared by a Fischer-Tropsch methane condensation reaction using a hydrogen/carbon monoxide ratio of less than 2.5, preferably less than 1.75, more preferably from 0.4 to 1.5, and ideally using a cobalt containing catalyst. Suitably it will have been obtained from a hydrocracked Fischer-Tropsch synthesis product (for instance as described in GB-B-2077289 and/or EP-A-0147873), or more preferably a product from a two-stage hydroconversion process such as that described in EP-A-0583836 (see above). In the latter case, preferred features of the hydroconversion process may be as disclosed at pages 4 to 6, and in the examples, of EP-A-0583836.

The kerosene fuel composition of the present invention preferably contains no more than 3000 ppmw sulphur, more preferably no more than 2000 ppmw, or no more than 1000 ppmw, or no more than 500 ppmw sulphur.

The kerosene fuel composition or the components thereof may be additivated (additive-containing) or unadditivated (additive-free). If additivated, e.g. at the refinery or in later stages of fuel distribution, it will contain minor amounts of one or more additives selected for example from anti-static agents (e.g. STADIS™ 450 (ex. Octel)), antioxidants (e.g. substituted tertiary butyl phenols), metal deactivator additives (e.g. N,N′-disalicylidene 1,2-propanediamine), fuel system icing inhibitor additives (e.g. diethylene glycol monomethyl ether), corrosion inhibitor/lubricity improver additives (e.g. APOLLO™ PRI 19 (ex. Apollo), DCI 4A (ex. Octel), NALCO™ 5403 (ex. Nalco)), or thermal stability improving additives (e.g. APA 101™, (ex. Shell)) that are approved in international civil and/or military jet fuel specifications.

Unless otherwise stated, the (active matter) concentration of each such additional component in the additivated kerosene fuel composition is at levels required or allowed in international jet fuel specifications.

In the above, amounts (concentrations, % v, ppmw, wt %) of components are of active matter, i.e. exclusive of volatile solvents/diluent materials, unless otherwise stipulated in the relevant specification.

The kerosene fuel composition of the present invention is particularly applicable where the kerosene fuel composition is used or intended to be used in a jet engine.

Diesel Fuel Compositions

The diesel fuel composition according to the present invention typically comprise mixtures of hydrocarbons boiling in the range from 130 to 410° C., more typically in the range of from 150 to 400° C. The initial boiling point of the diesel fuel compositions according to the present invention are in the range of from 130 to 230° C. (IP123), preferably in the range of from 140 to 220° C., more preferably in the range of from 150 to 210° C. The final boiling point of the diesel fuel compositions according to the present invention is at most 410° C., preferably at most 405° C., more preferably at most 400° C.

In addition to the component having at least one C₄₊ compound derivable from a water-soluble oxygenated hydrocarbon, the diesel fuel composition may comprise a mixture of two or more different diesel fuel components, and/or be additivated as described below.

Such diesel fuel compositions will contain one or more base fuels which may typically comprise liquid hydrocarbon middle distillate gas oil(s), for instance petroleum derived gas oils. Such fuels will typically have boiling points within the range described above, depending on grade and use. They will typically have a density from 750 to 1000 kg/m³, preferably from 780 to 860 kg/m³, at 15° C. (e.g. ASTM D4502 or IP 365) and a cetane number (ASTM D613) of from 35 to 120, more preferably from 40 to 85. They will typically have an initial boiling point in the range described above and a final boiling point of at most 410° C., preferably at most 405° C., more preferably at most 400° C., most preferably in the range 290 to 400° C. Their kinematic viscosity at 40° C. (ASTM D445) might suitably be from 1.2 to 4.5 mm²/s.

An example of a petroleum derived gas oil is a Swedish Class 1 base fuel, which will have a density from 800 to 820 kg/m³ at 15° C. (SS-EN ISO 3675, SS-EN ISO 12185), a T95 of 320° C. or less (SS-EN ISO 3405) and a kinematic viscosity at 40° C. (SS-EN ISO 3104) from 1.4 to 4.0 mm²/s, as defined by the Swedish national specification EC1.

Optionally, non-mineral oil based fuels, such as biofuels (other than the component having at least one C₄₊ compound derivable from a water-soluble oxygenated hydrocarbon) or Fischer-Tropsch derived fuels, may also form or be present in the diesel fuel. Such Fischer-Tropsch fuels may for example be derived from natural gas, natural gas liquids, petroleum or shale oil, petroleum or shale oil processing residues, coal or biomass.

The amount of Fischer-Tropsch derived fuel used in the diesel fuel composition of the present invention may be from 0% to the remaining portion of the diesel fuel composition (i.e. the portion of the diesel fuel composition that is not the component having at least one C₄₊ compound derivable from a water-soluble oxygenated hydrocarbon), preferably from 5% to the remaining portion of the diesel fuel composition, more preferably from 5% to 75% v of the diesel fuel composition. It may be desirable for such a diesel fuel composition to contain 10% v or greater, more preferably 20% v or greater, still more preferably 30% v or greater, of the Fischer-Tropsch derived fuel. It is particularly preferred for such diesel fuels to contain 30 to 75% v, and particularly 30 or 70% v, of the Fischer-Tropsch derived fuel. The balance of the diesel fuel is made up of the component having at least one C₄₊ compound derivable from a water-soluble oxygenated hydrocarbon and optionally one or more other diesel fuel components.

Such a Fischer-Tropsch derived fuel component is any fraction of the middle distillate fuel range, which can be isolated from the (optionally hydrocracked) Fischer-Tropsch synthesis product. Typical fractions will boil in the naphtha, kerosene or gas oil range. Preferably, a Fischer-Tropsch product boiling in the kerosene or gas oil range is used because these products are easier to handle in for example domestic environments. Such products will suitably comprise a fraction larger than 90 wt % which boils between 160 and 400° C., preferably to about 370° C. Examples of Fischer-Tropsch derived kerosene and gas oils are described in EP-A-0583836, WO-A-97/14768, WO-A-97/14769, WO-A-00/11116, WO-A-00/11117, WO-A-01/83406, WO-A-01/83648, WO-A-01/83647, WO-A-01/83641, WO-A-00/20535, WO-A-00/20534, EP-A-1101813, U.S. Pat. No. 5,766,274, U.S. Pat. No. 5,378,348, U.S. Pat. No. 5,888,376 and U.S. Pat. No. 6,204,426.

The Fischer-Tropsch product will suitably contain more than 80 wt % and more suitably more than 95 wt % iso and normal paraffins and less than 1 wt % aromatics, the balance being naphthenics compounds. The content of sulphur and nitrogen will be very low and normally below the detection limits for such compounds. For this reason the sulphur content of a diesel fuel composition containing a Fischer-Tropsch product may be very low.

The diesel fuel composition preferably contains no more than 5000 ppmw sulphur, more preferably no more than 500 ppmw, or no more than 350 ppmw, or no more than 150 ppmw, or no more than 100 ppmw, or no more than 70 ppmw, or no more than 50 ppmw, or no more than 30 ppmw, or no more than 20 ppmw, or most preferably no more than 15 ppmw sulphur.

The diesel fuel typically also includes one or more fuel additive.

The diesel base fuel may itself be additivated (additive-containing) or unadditivated (additive-free). If additivated, e.g. at the refinery, it will contain minor amounts of one or more additives selected for example from anti-static agents, pipeline drag reducers, flow improvers (e.g. ethylene/vinyl acetate copolymers or acrylate/maleic anhydride copolymers), lubricity additives, antioxidants and wax anti-settling agents.

Detergent-containing diesel fuel additives are known and commercially available. Such additives may be added to diesel fuels at levels intended to reduce, remove, or slow the build up of engine deposits.

Examples of detergents suitable for use in diesel fuel additives for the present purpose include polyolefin substituted succinimides or succinamides of polyamines, for instance polyisobutylene succinimides or polyisobutylene amine succinamides, aliphatic amines, Mannich bases or amines and polyolefin (e.g. polyisobutylene) maleic anhydrides. Succinimide dispersant additives are described for example in GB-A-960493, EP-A-0147240, EP-A-0482253, EP-A-0613938, EP-A-0557516 and WO-A-98/42808. Particularly preferred are polyolefin substituted succinimides such as polyisobutylene succinimides.

The diesel fuel additive mixture may contain other components in addition to the detergent. Examples are lubricity enhancers; dehazers, e.g. alkoxylated phenol formaldehyde polymers; anti-foaming agents (e.g. polyether-modified polysiloxanes); ignition improvers (cetane improvers) (e.g. 2-ethylhexyl nitrate (EHN), cyclohexyl nitrate, di-tert-butyl peroxide and those disclosed in U.S. Pat. No. 4,208,190 at column 2, line 27 to column 3, line 21); anti-rust agents (e.g. a propane-1,2-diol semi-ester of tetrapropenyl succinic acid, or polyhydric alcohol esters of a succinic acid derivative, the succinic acid derivative having on at least one of its alpha-carbon atoms an unsubstituted or substituted aliphatic hydrocarbon group containing from 20 to 500 carbon atoms, e.g. the pentaerythritol diester of polyisobutylene-substituted succinic acid); corrosion inhibitors; reodorants; anti-wear additives; anti-oxidants (e.g. phenolics such as 2,6-di-tert-butylphenol, or phenylenediamines such as N,N′-di-sec-butyl-p-phenylenediamine); metal deactivators; combustion improvers; static dissipator additives; cold flow improvers; and wax anti-settling agents.

The diesel fuel additive mixture may contain a lubricity enhancer, especially when the diesel fuel composition has a low (e.g. 500 ppmw or less) sulphur content. In the additivated diesel fuel composition, the lubricity enhancer is conveniently present at a concentration of less than 1000 ppmw, preferably between 50 and 1000 ppmw, more preferably between 70 and 1000 ppmw. Suitable commercially available lubricity enhancers include ester- and acid-based additives. Other lubricity enhancers are described in the patent literature, in particular in connection with their use in low sulphur content diesel fuels, for example in:

-   -   the paper by Danping Wei and H. A. Spikes, “The Lubricity of         Diesel Fuels”, Wear, III (1986) 217-235;     -   WO-A-95/33805—cold flow improvers to enhance lubricity of low         sulphur fuels;     -   WO-A-94/17160—certain esters of a carboxylic acid and an alcohol         wherein the acid has from 2 to 50 carbon atoms and the alcohol         has 1 or more carbon atoms, particularly glycerol monooleate and         di-isodecyl adipate, as fuel additives for wear reduction in a         diesel engine injection system;     -   U.S. Pat. No. 5,490,864—certain dithiophosphoric         diester-dialcohols as anti-wear lubricity additives for low         sulphur diesel fuels; and     -   WO-A-98/01516—certain alkyl aromatic compounds having at least         one carboxyl group attached to their aromatic nuclei, to confer         anti-wear lubricity effects particularly in low sulphur diesel         fuels.

It may also be preferred for the diesel fuel composition to contain an anti-foaming agent, more preferably in combination with an anti-rust agent and/or a corrosion inhibitor and/or a lubricity enhancing additive.

Unless otherwise stated, the (active matter) concentration of each such additive component in the additivated diesel fuel composition is preferably up to 10000 ppmw, more preferably in the range from 0.1 to 1000 ppmw, advantageously from 0.1 to 300 ppmw, such as from 0.1 to 150 ppmw.

The (active matter) concentration of any dehazer in the diesel fuel composition will preferably be in the range from 0.1 to 20 ppmw, more preferably from 1 to 15 ppmw, still more preferably from 1 to 10 ppmw, advantageously from 1 to 5 ppmw. The (active matter) concentration of any ignition improver present will preferably be 2600 ppmw or less, more preferably 2000 ppmw or less, conveniently from 300 to 1500 ppmw. The (active matter) concentration of any detergent in the diesel fuel composition will preferably be in the range from 5 to 1500 ppmw, more preferably from 10 to 750 ppmw, most preferably from 20 to 500 ppmw.

In the case of a diesel fuel composition, for example, the fuel additive mixture will typically contain a detergent, optionally together with other components as described above, and a diesel fuel-compatible diluent, which may be a mineral oil, a solvent such as those sold by Shell companies under the trade mark “SHELLSOL”, a polar solvent such as an ester and, in particular, an alcohol, e.g. hexanol, 2-ethylhexanol, decanol, isotridecanol and alcohol mixtures such as those sold by Shell companies under the trade mark “LINEVOL”, especially LINEVOL 79 alcohol which is a mixture of C₇₋₉ primary alcohols, or a C₁₂₋₁₄ alcohol mixture which is commercially available.

The total content of the additives in the diesel fuel composition may be suitably between 0 and 10000 ppmw and preferably below 5000 ppmw.

In the above, amounts (concentrations, % vol, ppmw, % wt) of components are of active matter, i.e. exclusive of volatile solvents/diluent materials.

Process of Preparing a Liquid Fuel Composition

The liquid fuel composition of the present invention is produced by admixing:

(a) a component derivable from a water-soluble oxygenated hydrocarbon, with (b) at least one fuel component.

By the term “fuel component” it is meant a component used in the preparation of a liquid fuel composition, or a liquid fuel composition per se, which is not a component derived from a water soluble oxygenated hydrocarbon. Examples of “fuel components” include fuel components that are currently used in the preparation of gasoline, kerosene and/or diesel fuel, such as petroleum derived product streams, Fischer-Tropsch derived product streams, oxygenates and biofuel components.

Typically, the petroleum derived product streams are product streams produced at an oil refinery, also referred to herein as refinery streams. Non-limiting examples of such refinery streams include:

-   -   “C_(4s)” (light boiling fraction typically comprising greater         than 80% vol paraffinic and olefinic C₄ compounds)     -   Straight Run Tops (SR Tops) or Naphtha (light boiling fraction         of C₄-C₇ hydrocarbons (final boiling point below about 140° C.).         These hydrocarbons are mainly paraffins and have a low octane         rating. The stream is low in aromatics and has some naphthenes.)     -   Isomerate (light boiling fraction (final boiling point below         about 110° C.) obtained by isomerising C₅ and C₆ paraffins in SR         Tops/Naphtha to produce higher octane isomers)     -   Light, full-range (FR) or heavy Platformate (or light,         full-range (FR) or heavy Reformate) (fraction obtained by         catalytic reforming of hydrotreated naphtha to produce a high         octane, high aromatic, low olefin stream)     -   Alkylate (including aviation alkylate) (fraction produced by the         alkylation of isobutane with C₄ and C₃ olefins to produce         high-octane branched chain paraffins)     -   Light or heavy catalytic cracked gasoline (LCCG or HCCG)         (fraction produced by the treatment of heavier streams in a         fluidised catalytic cracker to produce lighter hydrocarbons,         including olefins)     -   Straight run kerosene (fraction containing high levels of         paraffinic hydrocarbons, typically having a distillation         temperature in the range of from about 150° C., +/−10° C., to         about 260° C., +/− about 20° C.)     -   Sweetened kerosene (straight run kerosene that has been treated         to reduce mercaptan levels and also reduce total acid content)     -   Hydrotreated or hydrofined kerosene (mildly hydroprocessed         straight run kerosene that has reduced mercaptan, sulphur,         olefins, acid and metals levels)     -   Severely hydroprocessed kerosene (such as deeply hydrogenated         kerosene, hydrodesulphurised kerosene, hydrocracked kerosene         (straight run kerosene that has been subjected to a more severe         hydroprocessing than hydrotreated kerosene, typically leading to         lower sulphur and nitrogen levels))     -   Straight run distillates boiling in the diesel fuel range     -   Hydrocracked gas oil (AGO)     -   Light cracked and hydrotreated oils from the coker     -   Catalytically cracked gas oil (VGO)     -   Thermally and steam cracked gas oils

The oxygenates and biofuel components are any such component which is suitable for use in a liquid fuel composition, such as those described hereinbefore.

Process of Preparing a Gasoline Composition

In order to prepare a gasoline composition of the present invention, a component derivable from a water-soluble oxygenated hydrocarbon, as described above, in particular the lighter fraction of a component derived from a water-soluble oxygenated hydrocarbon, is combined with at least one fuel component.

Typical fuel components which may be admixed with the component derivable from a water-soluble oxygenated hydrocarbon to prepare a gasoline composition according to the present invention include:

-   -   Gasoline compositions per se;     -   Refinery streams, such as C_(4s), SR Tops, Isomerate, Light         Platformate, FR Platformate, Heavy Platformate, Alkylate, LCCG         and HCCG;     -   Oxygenates, such as alcohols and ethers. Preferred oxygenate         components include methanol, ethanol, propanol, butanol, methyl         tertiary-butyl ether (MTBE), and ethyl tertiary-butyl ether         (ETBE); and     -   Biofuel components such as those described hereinbefore.

By the term “gasoline composition” when used in reference to a fuel component, it is meant a composition as defined in the gasoline composition section above.

Typically, a gasoline composition of the present invention is prepared by admixing:

-   (a) the lighter fraction of a component derived from a water-soluble     oxygenated hydrocarbon as described above, with -   (b) at least one fuel component selected from a refinery stream.

Preferably, a gasoline composition of the present invention is prepared by admixing:

-   (a) the lighter fraction of a component derived from a water-soluble     oxygenated hydrocarbon as described above, with -   (b) at least one fuel component selected from the refinery streams     C_(4s), SR Tops, Isomerate, Light Platformate, FR Platformate, Heavy     Platformate, Alkylate, LCCG and HCCG; and optionally an oxygenate     selected from ethanol, MTBE and ETBE.

More preferably, a gasoline composition of the present invention is prepared by admixing:

-   (a) the lighter fraction of a component derived from a water-soluble     oxygenated hydrocarbon as described above, with -   (b) at least one fuel component selected from the refinery streams     C_(4s), SR Tops, Heavy Platformate, Alkylate and LCCG; and     optionally ethanol.

Depending upon the amount of the lighter fraction of a component derived from a water-soluble oxygenated hydrocarbon that is used, the amount of the fuel components used will be varied to prepare a gasoline composition having the desired properties.

For instance, a gasoline composition of the present invention may be prepared by admixing:

-   (a) at least 0.1% vol based on the overall fuel composition of the     lighter fraction of a component derived from a water-soluble     oxygenated hydrocarbon as described above, with -   (b) at least one fuel component selected from the refinery streams     in the following amounts, 1 to 15% vol C_(4s), 3 to 25% vol SR Tops,     0 to 50% vol Heavy Platformate, 5 to 20% vol Alkylate, and 10 to 35%     vol LCCG, based on the overall fuel composition; and optionally up     to 85% ethanol, based on the overall fuel composition.

In the preparation of the gasoline compositions according to the present invention, it may be desirable to reduce the relative amount of any SR Tops and/or Heavy Platformate in the gasoline composition according to the present invention with increasing amounts of the lighter fraction of a component derived from a water-soluble oxygenated hydrocarbon as described above. Therefore, a gasoline composition of the present invention may be prepared by substituting at least a portion of any SR Tops and/or Heavy Platformate used in the preparation of a gasoline with the lighter fraction of a component derived from a water-soluble oxygenated hydrocarbon as described above.

Alternatively, a gasoline composition of the present invention is prepared by admixing:

-   (a) the lighter fraction of a component derived from a water-soluble     oxygenated hydrocarbon as described above, with -   (b) a gasoline composition.

If the gasoline composition being prepared is an aviation gasoline, then no oxygenates would be used in the preparation of such an aviation gasoline according to the present invention.

Process of Preparing a Kerosene Composition

In order to prepare a kerosene composition of the present invention, a component derivable from a water-soluble oxygenated hydrocarbon, as described above, in particular the moderate fraction of a component derived from a water-soluble oxygenated hydrocarbon, is combined with at least one fuel component.

Typical fuel components which may be admixed with the component derivable from a water-soluble oxygenated hydrocarbon to prepare a kerosene composition according to the present invention include refinery streams, such as straight run kerosene, sweetened kerosene, hydrotreated or hydrofined kerosene, and severely hydroprocessed kerosene.

Typically, a kerosene composition of the present invention is prepared by admixing:

-   (a) the moderate fraction of a component derived from a     water-soluble oxygenated hydrocarbon as described above, with -   (b) at least one fuel component selected from the refinery streams     straight run kerosene, sweetened kerosene, hydrotreated or     hydrofined kerosene, and severely hydroprocessed kerosene.

Process of Preparing a Diesel Fuel Composition

In order to prepare a diesel fuel composition of the present invention, a component derivable from a water-soluble oxygenated hydrocarbon, as described above, in particular the heavier fraction of a component derived from a water-soluble oxygenated hydrocarbon, is combined with at least one fuel component.

Typical fuel components which may be admixed with the component derivable from a water-soluble oxygenated hydrocarbon to prepare a diesel fuel composition according to the present invention include:

-   -   Diesel fuel compositions per se;     -   Refinery streams, such as straight run distillates boiling in         the diesel fuel range, hydrocracked gas oil (AGO), light cracked         and hydrotreated oils from the coker, catalytically cracked gas         oil (VGO), thermally and steam cracked gas oils;     -   Biofuel components such as those described hereinbefore.

By the term “diesel fuel composition” when used in reference to a fuel component, it is meant a composition as defined in the diesel fuel composition section above.

Typically, a diesel fuel composition of the present invention is prepared by admixing:

-   (a) the heavier fraction of a component derived from a water-soluble     oxygenated hydrocarbon as described above, with -   (b) at least one fuel component selected from a refinery stream.

Preferably, a diesel fuel composition of the present invention is prepared by admixing:

-   (a) the heavier fraction of a component derived from a water-soluble     oxygenated hydrocarbon as described above, with -   (b) at least one fuel component selected from the refinery streams     straight run distillates boiling in the diesel fuel range,     hydrocracked gas oil (AGO), light cracked and hydrotreated oils from     the coker, catalytically cracked gas oil (VGO), thermally and steam     cracked gas oils; and optionally a bifuel component.

The present invention further provides a method of operating an internal combustion engine, jet engine, or a boiler, which method involves introducing into a combustion chamber of the engine or boiler, a liquid fuel composition according to the present invention.

The present invention will be further understood from the following examples.

EXAMPLES Exemplary Reactor Systems Example 1

FIG. 8 shows a process diagram illustrating one reactor system useful in practicing the present invention. A feedstock tank 1 acts as a reservoir for holding the feedstock solutions. The feedstock solution is delivered from the feedstock tank 1 to feed pump 3 through feed line 2, where it is then passed through discharge line 4 to preheater 5. The preheater 5 may be a heat exchanger heated by an electrical resistance heater, or any other heat exchanger known in the art. The preheated feed is then passed through line 6 and, in some cases, combined with hydrogen 7 before entering reactor 9 through line 8. One illustration of a potential reactor 9 is set forth in FIG. 11 and more fully described in Example 4 below.

The temperature of the walls of reactor 9 is maintained by block heaters, 10 a, 10 b, 10 c, and 10 d, in this case, electrical resistance heaters. Upon exiting the reactor 9, reaction products enter the reactor outlet line 11 and are cooled to near ambient temperature in reactor product cooler 12, resulting in a potential three phase product stream. From reactor product cooler 12, the reaction products proceed through line 13 to pressure regulating valve 14, which is used to control the pressure at the reactor outlet if required.

After valve 14, the products enter a phase separator 16 through line 15 where it segregates into three separate phases: (1) non-condensable gas components 17 containing predominately hydrogen, carbon dioxide, methane, ethane, and propane; (2) an organic liquid fraction 18 containing both hydrocarbons and C₃₋₃₀ alcohols, ketones and carboxylic acids; and (3) an aqueous layer 19 containing mostly water and water soluble oxygenated compounds, such as ethanol, isopropanol, acetone, propanol and acetic acid. The non-condensable gas fraction 17 may be routed through the gas product line 20 to pressure reducing valve 21. The pressure of separator 16 is maintained by pressure reducing valve 21. In an alternate mode of operation, the separator 16 may be maintained at a pressure nearly the same as the reactor outlet by opening or eliminating valve 14. In the alternate mode of operation, the reactor outlet pressure is then controlled by action of pressure reducing valve 21. Gas flow rate and composition are measured upon exiting the system through line 22.

The organic liquid fraction 18 exits the separator through line 23 before entering organic draw-off valve 24. The level of organic phase within the separator is controlled by adjustment of valve 24. The flow rate and composition of the organic fraction are determined after the organic fraction exit the system through line 25. The aqueous liquid fraction 19 exits the separator through line 26 before entering separator bottoms draw-off valve 27. The level of aqueous phase within the separator is controlled by adjustment of valve 27.

The flow rate and composition of the aqueous fraction may be determined after the aqueous fraction exits the system through line 28. In an alternate mode of operation, both the organic liquid fraction 18 and the aqueous liquid fraction 19 exit the system through the bottom draw-off valve 27 of the separator and line 28 before being separated in a decanter for measurement of the individual phase compositions and flow rates.

In all cases, the alternate modes of operation do not affect the catalytic processes being investigated. The alternate modes of operation may be employed as deemed prudent to achieve optimal control of the process, depending on the relative flow rates of the gaseous phase 17, organic liquid phase 18, and aqueous phase 19.

Prior to initiating a flow of feed to the reactors, unless otherwise noted, catalysts were reduced in a stream of flowing hydrogen at 400° C., regardless of whether a reduction was completed prior to loading the catalyst into the reactors.

Example 2

FIG. 9 shows a process diagram illustrating another reactor system useful for practicing the present invention. This reactor configuration contains two separate reactors with the capability of operating both reactors in series or operating only the first reactor. In addition, this configuration allows the catalyst in the second reactor to be taken off line and regenerated in situ. After regeneration, the second reactor may be returned to service without impacting the first reactor operation.

The reactor is similar to the reactor of Example 1, except that the reaction products from reactor product cooler 12 could be routed into the second reactor through line 14 or routed to bypass the second reactor by passing into line 44. When utilizing the second reactor, flow would proceed from line 14 to pressure regulating valve 15. Pressure regulating valve 15 may be used to control the pressure at the outlet of the first reactor. From pressure regulating valve 15 the flow proceeds to the second reactor inlet isolation valve 17 and into line 18. From line 18 the flow continues to line 19 and into the second reactor preheater 20. In the illustrated embodiment, preheater 20 is a heat exchanger heated by an electrical resistance heater.

The preheated feed is then passed through line 19 into the second reactor 22, which is more fully described in Example 4. The temperature of the wall of reactor 22 is maintained by block heaters, 23 a, 23 b, 23 c, and 23 d, in this case, electrical resistance heaters. Upon exiting the reactor, the reaction products enter the second reactor outlet line 24 and are then cooled in second reactor product cooler 25. From second reactor product cooler 26 the process flow may be routed through lines 26 and 27 to second reactor outlet isolation valve 28, into lines 29 followed by 30 and then into the product separator 31.

When operation of the second reactor is desired, valve 17 and valve 28 are open while the second reactor bypass valve 45 is closed to prevent the flow from bypassing the second reactor. When operation of only the first reactor is desired, or when the second reactor is being regenerated, valve 17 and valve 28 are closed while valve 45 is open. When the second reactor is bypassed, the first reactor product flows directly from line 13 into line 44, through bypass valve 45, into line 46 and on to line 30. In either case, whether the second reactor is in operation or bypassed, the flow would proceed from line 30 into the product separator.

In phase separator 31, reaction products are separated into a gaseous fraction 32, an organic fraction 33, and an aqueous fraction 34 as described above in Example 1. The gaseous fraction 32 is routed through the gas product line 35 to pressure reducing valve 36. The pressure of separator 31 is maintained by pressure reducing valve 36. When the second reactor 22 is in service, the pressure at the second reactor 22 outlet is controlled by action of pressure reducing valve 36. When the second reactor 22 is bypassed, the pressure at the outlet of the first reactor 9 is controlled by action of pressure reducing valve 36.

Gas flow rate and composition are measured upon exiting the system through line 37. The organic liquid fraction 33 exits the separator through line 38 before entering organic draw-off valve 39. The level of organic phase within the separator is controlled by adjustment of valve 39. The flow rate and composition of the organic fraction are determined after the organic fraction exits the system through line 40. The aqueous liquid fraction 34 exits the separator through line 41 before entering separator bottoms draw-off valve 42. The level of aqueous phase within the separator is controlled by adjustment of valve 42. The flow rate and composition of the aqueous fraction are determined after the aqueous fraction exits the system through line 43. In an alternate mode of operation, both the organic liquid fraction 33 and the aqueous liquid fraction 34 exit the system through the separator bottoms draw-off valve 42 and line 43 before being separated in a decanter for measurement of the individual phase compositions and flow rates. In all cases, the alternate modes of operation do not affect the catalytic processes being investigated. The alternate modes of operation are employed as deemed prudent to achieve optimal control of the process, depending on the relative flow rates of the gaseous phase 35, organic liquid phase 33, and aqueous phase 34.

Example 3

FIG. 10 shows a process diagram illustrating a dual feed pump reactor system useful for practicing the present invention. A dual feed pump system is used when the desired mix of feed components would not exist in a single liquid phase. For example, when a mix of 50% by weight 2-pentanol and 50% by weight water is the desired feed, two feed pumps are used, one to deliver 2-pentanol and the other to deliver water. A similar system may also be used to mix feedstock derived from two separate sources, such as a virgin feedstock and an oxygenated hydrocarbon feedstock derived from an effluent stream of the reactor system itself.

First feedstock tank 1 acts as a reservoir for a first feedstock solution, while second feedstock tank 40 acts as a reservoir for a second feedstock solution. A first feed is delivered from first feedstock tank 1 to first feed pump 3 through first feed line 2. The first feed is then passed through the first feed pump discharge line 4 to combined feed line 44. The second feed is delivered from the second feedstock tank 40 to second feed pump 42 through second feed line 41. The second feed is then passed through second feed pump discharge line 43 to combined feed line 44. From combined feed line 44 the combined feed passes into preheater 5. All other elements are as set forth in Example 1, except that the aqueous phase 19 may be recycled to feedstock tank 40 for further processing or used in other processes.

Example 4

FIG. 11 shows a schematic illustration of one type of reactor which may be employed in reactor systems as described in Examples 1, 2 and 3. Reactor tube 1 is composed of 316 stainless steel with either an inside diameter of 8.5 mms or an inside diameter of 21.2 mm, depending on the experiment. Inlet line 2 is provided to allow feedstock or intermediate product, such as oxygenates, to enter the reactor. Outlet line 3 is provided to remove product from the reactor. Inlet frit 4, composed of stainless steel, acts to secure the beds of preheat media and catalyst in place. Preheat media 5, consisting of stainless steel beads, acts as a zone to allow transfer of heat from the reactor walls so that the feed is at the desired temperature upon entering the catalyst 7. A stainless steel screen may be placed between preheat media 5 and catalyst 7 to prevent the materials from mixing. Catalyst 7 may be supported in position by a second stainless steel frit 8.

A thermowell 9 may be installed in some cases to allow measurement of the temperatures within catalyst 7 and preheating zone 5. Control of temperature at the reactor inlet is accomplished by the use of an external preheater prior to the feed entering the reactor through line 2, and may be further adjusted by control of the heat transfer that occurs in the preheat media. In some cases, the preheat media is not required to achieve the desired temperature profile. Control of the reactor wall temperature is achieved by the use of external heaters in contact with the outer wall of the reactor. Independently controlled heating zones may be used to control the temperature of the reactor wall as desired.

Example 5 Analysis Techniques

Product streams from the examples described below were analyzed as follows. The organic liquid phase was collected and analyzed using either gas chromatograph with mass spectrometry detection or flame ionization detection. Component separation was achieved using a column with a bonded 100% dimethyl polysiloxane stationary phase. Relative concentrations of individual components were estimated via peak integration and dividing by the sum of the peak areas for an entire chromatogram. Compounds were identified by comparison to standard retention times and/or comparison of mass spectra to a compiled mass spectral database. Gas phase compositions were determined by gas chromatography with a thermal conductivity detector and flame ionization or mass spectrometry detectors for other gas phase components. The aqueous fraction was analyzed by gas chromatography with and without a derivatization of the organic components of the fraction using a flame ionization detector. Product yields are represented by the feed carbon present in each product fraction. The weight hourly space velocity (WHSV) was defined as the weight of feed introduced into the system per weight of catalyst per hour, and based on the weight of the oxygenated hydrocarbon feed only, excluding water present in the feed.

Production of Oxygenates Example 6 Hydrogenation Catalyst

A hydrogenation catalyst was prepared by adding an aqueous solution of dissolved ruthenium nitrosyl nitrate to a carbon catalyst support (UU Carbon, Calgon, with particle sizes restricted to those that were maintained on a 120 mesh screen after passing through an 60 mesh screen) to a target loading of 2.5% ruthenium. Water was added in excess of the pore volume and evaporated off under vacuum until the catalyst was free flowing. The catalyst was then dried overnight at 100° C. in a vacuum oven.

Example 7 APR/Deoxygenation Catalyst

A combined APR and deoxygenation catalyst was prepared by dissolving hexachloroplatinic acid and perrhenic acid in water and then adding the mixture to a monoclinic zirconia catalyst support (NorPro Saint-Gobain, Product code SZ31164, with particle sizes restricted to those that were maintained on a 60 mesh screen after passing through an 18 mesh screen) using an incipient wetness technique to target a platinum loading of 1.8% and a rhenium loading of 6.3% on the catalyst after subsequent decomposition of the metal precursors. The preparation was dried overnight in a vacuum oven and subsequently calcined in a stream of flowing air at 400° C.

Example 8 Conversion of Sucrose to Oxygenates

The catalyst systems referenced in Examples 6 and 7 were investigated for the conversion of sucrose to an intermediate product containing oxygenates using the reactor system described in Example 1. The study was conducted using a 21.2 mm internal diameter stainless steel tube reactor shown in Example 4, with an analysis completed as described in Example 5.

31 grams of hydrogenation catalyst from Example 6 and 76 grams of APR catalyst from Example 7 were loaded into the reactor, with the hydrogenation catalyst on top of the APR catalyst, separated by a stainless steel screen. External hydrogen was combined with the feed prior to the feed entering the reactor. Heaters external to the reactor, shown in FIG. 8 as 10 a, 10 b, 10 c, 10 d, were maintained at the following reactor wall temperatures; 10 a-125° C., 10 b-200° C., 10 c-265° C., 10 d-265° C., resulting in reactor bed temperatures of approximately ˜110-150° C. for hydrogenation, and 150-265° C. for the APR/Deoxygenation catalyst. The ranges indicate the approximate reactor wall temperatures at the inlet and outlet of each catalyst bed, respectively. Results from the experiment across 39 hours of operation are shown in Table 1. The WHSV is based on the weight of the APR/Deoxygenation catalyst. Total mono-oxygenates includes alcohols, ketones, tetrahydrofurans and cyclic mono-oxygenates. Cyclic mono-oxygenates includes compounds in which the ring does not include oxygen, such as cyclopentanone and cyclohexanone. The fraction of feed carbon contained within unknown components in the aqueous phase was determined as the difference of carbon accounted for by known, measured components and the total organic carbon.

TABLE 1 Conversion of Sucrose to Oxygenates Across a Hydrogenation and APR Catalyst Hours on Stream 5 16 27 39 WHSV wt_(feed)/(wt_(catalyst) hr) 1.8 1.8 1.7 1.5 Added Hydrogen mol_(H2)/mol_(feed) 3.4 3.4 3.6 4.0 Organic Phase Yield % of feed carbon 27 25 20 22 Breakdown of Reactor Outlet Composition Carbon Dioxide % of feed carbon 19.4 21.2 18.1 17.7 Paraffins % of feed carbon 14.1 13.5 9.2 10.8 Mono-oxygenates % of feed carbon 31.5 30.6 27.5 30.8 Alcohols % of feed carbon 11.1 11.8 11.2 11.6 Ketones % of feed carbon 8.2 7.0 7.1 9.0 Tetrahydrofurans % of feed carbon 10.6 10.7 8.1 8.6 Cyclic % of feed carbon 1.6 1.1 1.1 1.5 Mono-oxygenates Unknown Aqueous % of feed carbon 21.2 27.8 28.3 32.0 Species

Example 9 APR/Deoxygenation Catalyst

A catalyst was prepared as described in Example 7, except that the catalyst support was a tetragonal zirconia (NorPro Saint-Gobain, Product code SZ61152) with particle sizes restricted to those that were maintained on a 60 mesh screen after passing through an 18 mesh screen.

Example 10 APR/Deoxygenation Catalyst

Hexachloroplatinic acid and perrhenic acid dissolved in water were added to a monoclinic zirconia catalyst support (NorPro Saint-Gobain, Product code SZ61164, with particle sizes restricted to those that were maintained on a 60 mesh screen after passing through an 18 mesh screen) using an incipient wetness technique to target a platinum loading of 1.9% and a rhenium loading of 1.8% on the catalyst after subsequent decomposition of the metal precursors. The preparation was dried overnight in a vacuum oven and subsequently calcined in a stream of flowing air at 400° C.

Example 11 APR/Deoxygenation Catalyst

A catalyst was prepared as described in Example 7 except that the support was a hydrogen peroxide functionalized activated carbon. The support was first prepared by adding activated carbon (Calgon UU 60×120 mesh carbon) slowly to a 30% hydrogen peroxide solution, with the mixture then left overnight. The aqueous phase was decanted and the carbon was washed three times with deionized water, and then dried under vacuum at 100° C. A solution of hexachloroplatinic acid and perrhenic acid in water was then added to the support using an incipient wetness technique to target a platinum loading of 1.8% and a rhenium loading of 6.3% after subsequent decomposition of the metal precursors. The preparation was dried overnight in a vacuum oven at 100° C.

Example 12 Conversion of Sorbitol and Glycerol

The catalyst systems referenced in Example 9, Example 10, and Example 11, were investigated for the conversion of sorbitol or glycerol to an intermediate product containing oxygenates using the reactor configuration described in Example 1, with an analysis completed as described in Example 5. The study was conducted using the 8.5 mm internal diameter stainless steel tube reactor shown in Example 4. In all cases, the reactor pressure was maintained at 625 psig. Reactor inlet and outlet temperatures, shown in Table 2 were controlled using heaters external to the reactor as shown in FIG. 8 as 10 a, 10 b, 10 c, 10 d. Results of these experiments are shown in Table 2.

Table 2 shows the impact of catalyst composition, feedstock composition, and operating conditions on the conversion performance. FIG. 12 shows the carbon number distribution of the mono-oxygenates produced in Experiment D and Experiment E. The primary difference between these two experiments was the reaction temperature. For Experiment D, mono-oxygenates containing three or fewer carbon atoms predominated while for Experiment E, a significant fraction of the mono-oxygenates contained four or more carbon atoms, indicating that condensation reactions were occurring within the same reaction zone as the hydrogen generation and deoxygenation reactions. The WHSV is based on the weight of the APR/Deoxygenation catalyst. The net hydrogen produced is the hydrogen present at the reactor outlet as H₂, which does not include hydrogen produced and consumed in situ. Total mono-oxygenates include alcohols, ketones, tetrahydrofurans and cyclic mono-oxygenates. Cyclic mono-oxygenates include compounds in which the ring does not include oxygen, such as cyclopentanone and cyclohexanone. The fraction of feed carbon contained within unknown components in the aqueous phase was determined as the difference of carbon accounted for by known, measured components and the total organic carbon.

TABLE 2 Conversion of Polyols to Oxygenates Across a APR/Deoxygenation Catalyst Experiment A B C D E Feed 50% 50% 65% 50% 50% Sorbitol Sorbitol Sorbitol Glycerol Glycerol Catalyst Composition Example No. 11 9 10 10 10 WHSV wt_(feed)/(wt_(catalyst) 2.1 1.8 1.7 1.5 1.5 hr) Catalyst Inlet Temp. ° C. 241 240 240 260 310 Catalyst Outlet ° C. 240 241 321 260 350 Temperature Net Hydrogen mol_(H2)/mol_(feed) 0.6 0.9 0.7 1.2 0.7 Produced Organic Phase Yield % of feed 17 24 38 0 38 carbon Breakdown of Reactor Outlet Composition Carbon Dioxide % of feed 32.4 34.0 23.5 31.3 16.0 carbon Paraffins % of feed 37.4 25.3 7.8 6.6 7.4 carbon Total Mono-oxygenates % of feed 33.9 32.9 40.0 45.9 41.0 carbon Alcohols % of feed 6.3 8.5 2.6 40.6 4.6 carbon Ketones % of feed 23.5 16.9 15.2 5.2 24.1 carbon Tetrahydrofurans % of feed 4.1 7.2 10.7 0.1 2.7 carbon Cyclic % of feed 0.0 0.4 11.6 0.0 9.7 Mono-oxygenates carbon Unknown Aqueous % of feed 1.2 7.8 15.8 30.4 10.7 Species carbon

Condensation of Oxygenates Using Basic Catalysts Example 13

A zinc aluminate catalyst support was prepared by mixing zinc oxide powder and alumina powder (Dispal 18N4-80, Sasol North America, Houston, Tex.) to a target ratio of 1.0 moles of ZnO to 1 mole of Al₂O₃. Dilute nitric acid was then added at a level of 1 wt % HNO₃ to alumina. The dough consistency of the mixture was adjusted with water addition to form a workable dough, which was then extruded using a laboratory scale extruder. The extrudates were dried overnight under vacuum at 100° C., then further dried at 200° C. for one hour under flowing air, and then subsequently calcined at 750° C. for 4 hours under flowing air. The resulting material was then ground and sieved. Material that was maintained on a 60 mesh screen after passing through an 18 mesh screen was recovered.

Example 14

Hexachloroplatinic acid was added to the calcined material of Example 13 using an incipient wetness impregnation technique to achieve a target platinum loading of 1.0 wt %. The catalyst was dried overnight under vacuum at 100° C. and calcined at 400° C. under flowing air.

Example 15

Palladium nitrate was added to the calcined material of Example 13 using an incipient wetness impregnation technique to achieve a target palladium loading of 0.5 wt %. The catalyst was dried overnight under vacuum at 100° C. and calcined at 400° C. under flowing air.

Example 16

A copper zinc aluminate catalyst was prepared by mixing zinc oxide, copper (I) oxide, and alumina powder (Dispal 18N4-80) at a target ratio of 0.11 moles of CuO and 0.9 moles of ZnO to one mole of Al₂O₃. Dilute nitric acid was then added at a level of 1 wt % HNO₃ to alumina. The dough consistency of the mixture was adjusted with water addition to form a workable dough, which was then extruded using a laboratory scale extruder. The extrudates were dried overnight under vacuum at 100° C., then further dried at 200° C. for one hour under flowing air, and then subsequently calcined at 750° C. for 4 hours under flowing air. The resulting material was then ground and sieved. Material that was maintained on a 60 mesh screen after passing through an 18 mesh screen was recovered.

Example 17

A cesium modified silica-alumina catalyst was prepared by adding cesium carbonate dissolved in water to Siralox silica-alumina catalyst support (Sasol North America, Houston, Tex.). The target loading of cesium was 25 wt % based on final catalyst weight. This material was dried for 24 hours under vacuum at 100° C. and calcined at 500° C. for 6 hours under flowing air. After calcining, platinum was added using an incipient wetness impregnation technique to achieve a final platinum loading of 1 wt %. After impregnation, the catalyst was dried and then calcined at 500° C. for 6 hours under flowing air.

Example 18

A cerium modified silica was prepared by adding cerium nitrate solution to a silica gel (Davisil grade 636, WR Grace Company) to a final loading of 25 wt % CeO₂. The resulting material was then dried at 120° C. for six hours and further calcined at 550° C. for six hours under flowing air. Palladium nitrate was added to the calcined material using an incipient wetness impregnation technique to achieve a target palladium loading of 0.5 wt %. This material was then dried at 120° C. for six hours and further calcined at 550° C. for six hours under flowing air.

Example 19

The catalyst systems referenced in Examples 14-18 were investigated for the vapor-phase condensation of various oxygenates. The studies were conducted using 8.5 mm and 21.2 mm internal diameter size stainless steel tube reactors as described in Example 4 and in the reactor systems illustrated by FIGS. 8 and 10. Between 15 and 18 milliliters of catalyst was loaded into the smaller reactor, with between 50 and 70 milliliters of catalyst loaded into the larger reactor. In all cases the catalyst was reduced at 400° C. under flowing hydrogen prior to use.

The organic liquid phase was collected and analyzed as described in Example 5. Table 3 shows organic product yields and composition as a function of operating conditions, feedstock composition, and the added metal component for the catalysts described in Examples 14-18 above. Greater than 100% reported organic phase yields stem from experimental uncertainty in the measurement of process stream flow rates or composition. Non-condensed components are those components that do not require the formation of new carbon-carbon bonds to be produced from the given feed. For simplicity, all compounds containing five or fewer carbon atoms are considered to be non-condensed components. Total condensation products are those compounds containing six or more carbon atoms, which require the formation of new carbon-carbon bonds to be formed from the given feedstocks.

Experiments F and G demonstrate that product selectivity can be affected by the choice of hydrogenation function, e.g. Pt or Pd. Paraffins were produced to a larger extent over the catalyst containing 1% platinum compared to the catalyst containing 0.5% palladium. The later favored the production of mono-oxygenates, primarily ketones. Experiments H and I further reinforce this concept. Experiment H shows that condensed mono-oxygenate components can be obtained at high yield with isopropyl alcohol as a feed, accounting for >97% of the organic product and containing >90% of the overall carbon at the reactor outlet. By increasing the reaction temperature and using copper to drive the hydrogenation reactions, the selectivity can be shifted to obtain a significant yield of olefins (Experiment I). Experiments J, K and L show that a number of other heterogeneous catalysts can be used to promote the condensation of oxygenates followed by hydrogenation of the initial condensation products. Experiments K and L show that as the temperature is decreased from 300° C. to 250° C., the rate of condensation drops so that the conversion to condensed products drops from 81 wt % to 18 wt % in the resulting organic phase.

TABLE 3 Vapor Phase Condensation of Oxygenates Over Basic Catalysts Catalyst 1% Pt/Cs Impregnated 0.5% Pd/ 0.5% Pd/ 1% Pt/ 0.5% Pd/ 0.5% Pd/ Siralox Ce Modified Ce Modified ZnO/Al2O3 ZnO/Al2O3 ZnO/Al2O3 CuO/ZnO/Al2O3 Silica-Alumina Silica Silica Experiment F G H I J K L Feed Feed A Feed A Feed B Feed B Feed A Feed B Feed B WHSV wt_(feed)/(wt_(cat) 1 1.5 1.5 2 1.1 1.9 1.9 hr) Added mol_(H2)/mol_(feed) 1 1 0 0 1 0 0 Hydrogen Temperature ° C. 375 375 300 375 325 300 250 Pressure Psig 600 600 600 625 600 600 600 Organic Phase % of feed 75 99 95 55 107 74 98 Yield carbon Organic Phase Composition Breakdown C5− Hydrocarbons wt % 9.6 7.3 0.0 2.4 1.6 0.0 0.0 C5− Oxygenates wt % 6.2 20.9 1.9 14.6 75.8 18.5 81.8 Total Non- wt % 15.8 28.2 1.9 16.9 77.4 18.5 81.8 Condensed Components C6+ Paraffins wt % 49.5 18.9 0.3 1.0 0.0 20.1 0.2 C6+ Olefins wt % 4.6 0.0 0.0 15.9 0.0 0.0 0.0 Other C6+ wt % 0.0 0.0 0.0 1.1 0.0 0.0 0.0 Hydrocarbons C6+ Mono- wt % 30.2 51.8 97.3 64.5 22.6 61.0 18.0 oxygenates Total Cond. wt % 84.2 70.7 97.6 82.5 22.6 81.1 18.2 Products Feed A - 49.5% 2-Pentanone, 50.5% 2-Pentanol Feed B - 100% Isopropyl Alcohol

Condensation of Oxygenates Using Acid-Base Catalysts Example 20

A hydrotalcite catalyst was prepared from a commercially available hydrotalcite support (ESM-350, ASM Catalysts, Baton Rouge, La.) by grinding the material and passing through graduated screens to achieve particles sizes larger than 60 mesh and less than 18 mesh. The material was then calcined in a quartz tube reactor at 450° C. for 6 hours under flowing nitrogen.

Example 21

Platinum was added to the hydrotalcite catalyst of Example 20 using an incipient wetness impregnation technique to achieve a final target platinum loading of 1 wt %. The platinum containing precursor was hexachloroplatinic acid, H₂PtCl₆. The impregnated material was dried overnight under vacuum at 100° C. and subsequently calcined at 400° C. for 2 hours under flowing air.

Example 22

Platinum and tin were added to the hydrotalcite catalyst of Example 20 using an incipient wetness impregnation technique to achieve a final target loading of 1 wt % Pt and 0.2 wt % Sn. The platinum containing precursor was hexachloroplatinic acid, H₂PtCl₆ while tin was derived from tin chloride, SnCl₂*2H₂O. The impregnated material was dried overnight under vacuum at 100° C. and subsequently calcined at 450° C. for 8 hours under flowing nitrogen.

Example 23

A 5% magnesium oxide catalyst supported on granular zirconia was prepared using an incipient wetness impregnation technique to achieve a final target loading of 5 wt % Mg. Magnesium was added as magnesium nitrate and dried overnight under vacuum at 100° C. and subsequently calcined at 450° C. for 8 hours under flowing air. An aqueous palladium nitrate solution was added to the calcined material to achieve a target palladium loading of 0.5 wt % using an incipient wetness impregnation technique. The catalyst was dried a second time and calcined at 400° C. for six hours under flowing air.

Example 24

A zinc aluminate catalyst support was prepared by mixing zinc oxide powder and alumina powder (Dispal 18N4-80, Sasol North America, Houston, Tex.) to a target ratio of 0.85 moles of ZnO to 1 mole of Al₂O₃. Dilute nitric acid was added at a level of 1 wt % HNO₃ to total solids. The dough consistency was adjusted with water addition to form a workable dough suitable for extrusion and the mixture was extruded using a laboratory scale extruder. The extrudates were dried overnight under vacuum at 100° C. and subsequently calcined at 750° C. for 8 hours under flowing air. The material was then sized to 18 by 60 mesh. An aqueous palladium nitrate solution was added to the calcined material to achieve a target palladium loading of 0.5 wt % using an incipient wetness impregnation technique. This catalyst was then dried a second time and calcined at 400° C. for six hours under flowing air.

Example 25

The catalyst systems referenced in Examples 21-24 were used to conduct vapor-phase condensation reactions with various oxygenates. The studies were conducted using 8.5 mm and 21.2 mm internal diameter size stainless steel tube reactors as described in Example 4 and reactor systems as illustrated in Examples 1 and 3. Between 15 and 18 milliliters of catalyst was loaded into the smaller reactor, with between 50 and 70 milliliters of catalyst loaded into the larger reactor. In all cases the catalyst was reduced at 400° C. under flowing hydrogen prior to use.

The organic liquid phase was collected and analyzed as described in Example 5. Table 4 shows the organic product yields and composition as a function of operating conditions, feedstock composition, and the added metal component for the hydrotalcite catalysts described in Examples 21 and 22 above. The data from the experiments show that a primarily hydrocarbon product can be formed from acetone and isopropyl alcohol in the absence of an added metal hydrogenation component. In Experiment M, the organic phase product contained primarily nine carbon methyl substituted cyclohexenes, categorized as other C₆₊ hydrocarbons in Table 4. The addition of platinum (Experiment N) to this catalyst favored the formation of condensed mono-oxygenate products, mainly ketones and alcohols, and the formation of some paraffins as a result of deoxygenation of the ketones and alcohols. The selectivity was further shifted in favor of condensed mono-oxygenates by attenuating the platinum with tin and operating at a higher pressure (Experiment O). Experiments P, Q, R and S illustrate the impact of reaction temperature for the condensation of a mixed feed containing pentanol and pentanone. As the reaction temperature was raised from 300° C. to 375° C., a gradual change in product composition became apparent, with the selectivity to condensed mono-oxygenates decreasing and the selectivity to condensed paraffins increasing as the temperature was raised.

Table 5 shows the impact of feedstock components and reaction temperature on organic product yields and composition for the catalysts of Examples 23 and 24. Experiments T and U compare the condensation of 2-pentanone and 2-methylterahydrofuran. Overall, the condensation of 2-pentanone is faster than 2-methyltetrahydrofuran. Nonetheless, around 30% of the tetrahydrofuran was converted to condensation products under these conditions. Experiments 10 and 11 show the impact of reaction temperature when using a pure isopropyl alcohol feed. At 300° C. (Experiment V), mono-oxygenated condensation products predominate, while at 400° C. (Experiment W) a significant portion of the products consisted of hydrocarbons. Compared to other experiments listed in Tables 4 and 5, Experiment W is notable in that the organic product contained a higher level of olefins. The addition of valeric acid to the feed (Experiment X) suppressed overall condensation rates and shifted the selectivity away from paraffins and towards other hydrocarbons, primarily substituted aryl compounds.

Greater than 100% reported organic phase yields stem from experimental uncertainty in the measurement of process stream flow rates or composition. Non-condensed components are those components that do not require the formation of new carbon-carbon bonds to be produced from the given feed. For simplicity, all compounds containing five or fewer carbon atoms are considered to be non-condensed components. Total condensation products are those compounds containing six or more carbon atoms, which require the formation of new carbon-carbon bonds to be formed from the given feedstocks.

TABLE 4 Vapor Phase Condensation of Oxygenates Over Hydrotalcite Catalysts Metal Function 1% Pt, 1% Pt, 1% Pt, 1% Pt, 1% Pt, None 1% Pt 0.2% Sn 0.2% Sn 0.2% Sn 0.2% Sn 0.2% Sn Experiment M N O P Q R S Feed Feed C Feed C Feed C Feed A Feed A Feed A Feed A WHSV wt_(feed)/wt_(cat) 1.0 0.9 0.7 0.7 0.7 0.7 0.7 hr Added mol_(H2)/mol_(feed) 0.5 0 0 1 1 1 1 Hydrogen Temperature ° C. 350 350 350 300 325 350 375 Pressure Psig 100 100 600 600 600 600 600 Organic Phase % of feed 61 95 91 108 104 108 85 Yield carbon Organic Phase Composition Breakdown C5− wt % 2.8 3.6 1.0 4.6 7.1 9.4 20.0 Hydrocarbons C5− Oxygenates wt % 11.9 16.0 5.8 41.9 21.4 13.7 8.8 Total Non- wt % 14.7 19.6 6.8 46.5 28.5 23.1 28.8 Condensed Components C6+ Paraffins wt % 0.0 13.1 7.6 2.2 11.3 28.6 53.0 C6+ Olefins wt % 5.1 1.2 1.0 0.0 0.2 0.0 0.0 Other C6+ wt % 72.8 0.0 0.0 0.0 0.0 0.0 0.0 Hydrocarbons C6+ Mono- wt % 5.7 54.3 80.4 51.4 60.1 47.8 18.2 oxygenates Total wt % 83.5 68.6 89.0 53.6 71.6 76.5 71.2 Condensation Products Feed A - 49.5% 2-Pentanone, 50.5% 2-Pentanol Feed C - 50% Isopropyl Alcohol, 50% Acetone

TABLE 5 Vapor Phase Condensation of Oxygenates Over Magnesium Impregnated Zirconia and Zinc Aluminate Catalysts Catalyst 0.5% Pd/Zinc 0.5% Pd/Zinc 0.5% Pd/Zinc Aluminate Aluminate Aluminate 0.5% Pd/5% 0.5% Pd/5% (0.85:1 (0.85:1 (0.85:1 Mg Zirconia Mg Zirconia ZnO:Al₂O₃) ZnO:Al₂O₃) ZnO:Al₂O₃) Experiment T U V W X Feed Feed D Feed E Feed B Feed B Feed F WHSV wt_(feed)/(wt_(cat) 2 2 1 1 1 hr) Added Hydrogen mol_(H2)/mol_(feed) 1 1 0 0 0 Temperature ° C. 400 400 300 400 400 Pressure psig 600 625 600 600 600 Organic Phase Yield % of feed 85 76 104 58 53 carbon Organic Phase Composition Breakdown C5− Hydrocarbons wt % 7.4 4.0 0.4 2.8 2.0 C5− Oxygenates wt % 21.4 66.5 5.2 6.9 17.3 Total Non-Condensed wt % 28.8 70.6 5.6 9.7 19.3 Components C6+ Paraffins wt % 22.1 10.9 3.4 17.1 5.6 C6+ Olefins wt % 0.0 2.8 0.0 23.8 13.6 Other C6+ Hydrocarbons wt % 1.3 0.3 0.0 8.1 19.8 C6+ Mono- wt % 46.5 14.7 90.8 41.2 38.6 oxygenates Total Cond. Products wt % 69.9 28.8 94.2 90.1 77.7 Feed B - 100% Isopropyl alcohol Feed D - 100% 2-pentanone Feed E - 100% 2-methyltetrahydrofuran Feed F - 90% Isopropyl alcohol, 10% Valeric Acid

Base Condensation of Oxygenates Followed by Deoxygenation Example 26

A zinc aluminate catalyst support was prepared similar to that in Example 13 except that the amount of zinc oxide was reduced to target a ratio of 0.85 moles of ZnO to 1 mole of Al₂O₃.

Example 27

Hexachloroplatinic acid was added to the calcined material of Example 26 using an incipient wetness impregnation technique to achieve a target platinum loading of 1.0 wt %. The catalyst was dried overnight under vacuum at 100° C. and calcined at 400° C. under flowing air.

Example 28

The catalyst systems referenced in Examples 27 and 15 were investigated for the vapor-phase condensation of various oxygenates and subsequent conversion to hydrocarbons. The studies were conducted using 21.2 mm internal diameter size stainless steel tube reactors as described in Example 4, and reactor systems as illustrated by Examples 2 and 3. Approximately 100 milliliters of each catalyst was loaded into two separate reactors. The two reactors were arranged so that the effluent of the first reactor flowed into the second reactor. The first reactor contained the catalyst of Example 15 and the second reactor contained the catalyst of Example 27. The catalyst was reduced at 400° C. under flowing hydrogen prior to use. In all cases, hydrogen was combined with the feed prior to entering the reactor.

Products were separated and analyzed as described in Example 5. Table 6 shows organic product yields and composition as a function of operating conditions and feedstock composition obtained from the consecutive reactions. Non-condensed components are those components that do not require the formation of new carbon-carbon bonds to be produced from the given feed. For simplicity, all compounds containing five or fewer carbon atoms are considered to be non-condensed components. Total condensation products are those compounds containing six or more carbon atoms, which require the formation of new carbon-carbon bonds to be formed from the given feedstocks.

Experiments AA, BB, CC, and DD demonstrate that various oxygenates can be employed in the consecutive condensation and deoxygenation reactions to yield a product containing primarily C₆₊ alkanes. The products contain a larger fraction of alkanes and low levels of oxygenated compounds compared to the results shown in Table 3. This demonstrates that the use of catalysts with different functionalities (i.e. a basic+hydrogenation catalyst in a first reactor followed by acid+basic+hydrogenation catalyst in the second reactor) can be more effective for the production of hydrocarbons from oxygenated compounds than the use of a catalyst that contains only basic and hydrogenation functionality. In Experiment EE, the organic product produced in Experiments AA through DD was recycled through the reaction system. After this treatment, the final product contained primarily alkanes with only traces of oxygen containing components. The hydrocarbons thus produced would be valuable for use as liquid fuels such as gasoline, diesel, and jet fuel.

TABLE 6 Vapor Phase Condensation and Deoxygenation of Oxygenates Experiment AA BB CC DD EE Feed Feed B Feed G Feed D Feed H Feed I WHSV wt_(feed)/(wt_(cat) 1.9 2.2 2.1 2.0 2.0 hr) Added mol_(H2)/mol_(feed) 1.5 1.7 2 2 >2 Hydrogen Reactor 1 ° C. 300 300 300 300 325 Temperature Reactor 2 ° C. 350 375 375 375 375 Temperature Pressure psig 625 625 625 625 625 Organic Phase % of feed 81 76 80 93 87 Yield carbon Product Composition Breakdown C5− % of feed 8 11 15 33 15 Hydrocarbons carbon C5− Oxygenates % of feed 3 2 2 4 0 carbon Total Non- % of feed 11 13 18 37 15 Condensed carbon Components C6+ Alkanes % of feed 71 71 65 56 74 carbon C6+ Alkenes % of feed 0 0 0 0 0 carbon Other C₆₊ % of feed 0 0 0 0 0 Hydrocarbons carbon C₆₊ Mono- % of feed 6 5 3 2 0 oxygenates carbon Total Products % of feed 77 76 68 58 74 (Condensation) carbon Feed B - 100% Isopropyl Alcohol Feed D - 100% 2-pentanone Feed G - 50% Isopropyl Alcohol, 50% 2-Pentanone Feed H - 50% Acetone, 50% 2-Pentanone Feed I - Organic Phase From AA-DD

Product Fractionation Example 29

The material of Experiment EE of Example 28 was collected and subjected to a distillation step. The distillation was conducted at atmospheric pressure using a simple, single stage laboratory batch distillation apparatus. 2.950 liters of liquid product was added to a heated round bottomed flask which acted at the reboiler at the beginning of the experiment. The overhead product was condensed and segregated into separate samples based on the temperature of the vapor phase in equilibrium with the boiling liquid, with an analysis of the fractions completed as described in Example 5. The carbon number distribution of the product fractions is shown in Table 7. All fractions contained primarily alkanes.

The fractions recovered with a boiling point less than 150° C. contain alkanes mainly in the C₅₋₁₀ range and would be suitable as a gasoline blending component. The higher boiling point range materials could be potentially useful for incorporation into distillate fuels, kerosene and diesel.

Example 30

The distilled product boiling in the range of 150° C. to 250° C. was analyzed for suitability as a Jet Fuel by a commercial testing service (Intertek Testing Services, Illinois) according to ASTM testing method D1655. The sample passed all required specifications with the exception of the flash point and density specifications. It is probable that the flash point specification could be met through adoption of improved product distillation, while the low density may be attributed to the high levels of alkanes in the sample.

TABLE 7 Results from Distillation of the Product of Example 30 Boiling Range Starting Less 100 to 150 to Greater ° C. Material than 100 150 250 than 250 Volume ml 2950 750 750 1300 180 Recovered Total wt % 99.8 100.0 100.0 99.4 91.4 Alkanes Carbon Breakdown by Species Carbon Number Number C⁴⁻ wt % 0.2 0.4 C₅₋₉ wt % 52.6 96.0 78.1 13.7 C₁₀₋₁₄ wt % 41.3 3.6 21.9 78.3 29.9 C₁₅₊ wt % 5.7 7.4 61.5

Production of C5+ Compounds from Glycerol Using a Single Catalytic System Example 31

A bimetallic catalyst system containing platinum and rhenium (5 wt % platinum with a molar ratio of Pt:Re of 1:2.5) supported on activated carbon (Calgon UU 60×120 mesh carbon) was prepared using incipient wetness techniques. Activated carbon was added slowly to a 30% hydrogen peroxide solution. After addition of the carbon was completed, the mixture was left overnight. The aqueous phase was decanted and the carbon was washed three times with of deionized water, and then dried under vacuum at 100° C. An aqueous solution, with a volume equal to incipient wetness volume for the carbon to be impregnated, 10.4 mL, and containing dihydrogen hexachloroplatinate (IV) hexahydrate (Alfa Aesar, 39.85% Pt) and perrhemic acid solution (Alfa Aesar, 76.41% HReO₄) was applied drop wise, while stirring, to hydrogen peroxide functionalized carbon. The wetted carbon was dried at 100° C. under vacuum.

Example 32

104.4 grams of the 1:2.5 Pt/Re catalyst were loaded into a 63.5 cm long reactor tube as described in Example 4 and Example 1, except that the temperature profile was controlled by heat exchange with a hot air stream provided by a blower and heater as illustrated in FIG. 7. The catalyst was reduced with flowing hydrogen at 350° C. for two hours before liquid feed was introduced to the catalyst bed. A 50 wt % glycerol (Colgate Palmolive USP Grade) containing about 20 ppm sulfate in water solution was fed downflow across the reactor after being preheated to 182° C. at a weight hourly space velocity of 0.97 grams of glycerol per gram of catalyst per hour. Hot air was fed upflow through the annular space at 409° C. The axial temperature profile within the center of the catalyst bed was measured using a sliding thermocouple as shown in Example 4, and is illustrated in FIG. 13. The separator pressure was maintained at 600 psig. The effluent from the reactor was cooled down with a water cooled condenser and separated in a three-phase separator. The gas-phase products were analyzed with a gas chromatograph that allowed the analysis of hydrogen, carbon dioxide, methane, ethane, propane, butane, pentane, and hexane. An organic phase was collected, weighed, and sent to Southwest Research Institute (San Antonio, Tex.) for gasoline analysis. The aqueous-phase was collected and weighed, and then analyzed using both a GCMS as well as GC-FID. In this system, there was complete conversion of the glycerol. Table 8 below shows the yields of hydrogen as well as the yields of carbon containing product compounds.

TABLE 8 Yields for the Conversion of Glycerol from Example 32 Products moles of H2/mole of glycerol feed 1.03 % Carbon/Carbon in Feed CO2 31.79 Methane 7.35 Ethane 7.28 Propane 5.25 Butane 0.56 Pentane 1.40 Hexane 2.05 C7-C13 Normal 0.87 C4-C13 Iso 2.87 C6-C12 Aromatic 3.87 C8-C11 Naphthalene/Napthenes 1.89 C5-C10 Olefins 5.67 C4-C6 Oxygenated Compounds in 1.86 Organic Phase Ethanol in Aqueous Phase 0.39 Acetic Acid in Aqueous Phase 1.33 Acetone in Aqueous Phase 13.19 Propionic Acid in Aqueous Phase 4.69 Propylene Glycol in Aqueous Phase 2.79 1-Propanol in Aqueous Phase 1.71 Isopropyl Alcohol in Aqueous Phase 1.28 C4/C5/C6 in Aqueous Phase 2.20

Production of C5+ Compounds from Sugar Alcohols Example 33

Experiments were conducted with aqueous solutions of oxygenated hydrocarbons (e.g., 50 wt. % glycerol/water mixture or 50 wt % sorbitol/water mixture) introduced in to the reactor system of Example 1. The feedstock was further modified by the addition of K₂SO₄ at various concentrations (1, 20, or 50 ppm).

Example 34

A total of 10.61 grams of the 1:2.5 Pt/Re catalyst were loaded into the 8.5 mm stainless steel reactor tube described in Example 4. The catalyst was reduced with flowing hydrogen at 350° C. for two hours before liquid feed was introduced to the catalyst bed. A 50 wt % glycerol solution containing about 1 ppm sulfate in water solution was fed downflow across the reactor at a WHSV of 1.24 grams of glycerol per gram of catalyst per hour. Subsequent tests were performed with 20 ppm and 50 ppm sulfate added as K₂SO₄. The block heaters were controlled at 260° C. and the separator pressure was maintained at 600 psig.

An organic phase was collected from the separated, weighed, and analyzed with a GC-MS as described in Example 5. Table 9 below shows the yields of hydrogen as well as the yields of carbon containing product compounds with the different amounts of sulfate added to the system. In this system, there was complete conversion of the glycerol. The table shows that a liquid organic phase was generated with the addition of sulfate greater than 20 ppm.

TABLE 9 Yields of Hydrogen and Carbon Containing Products from Example 34 K₂SO₄ loading Sulfate 1 20 50 Block 1 Temperature (° C.) 260 260 260 (FIG. 8, 10a) Block 2 Temperature (° C.) 260 260 260 (FIG. 8, 10b) Block 3 Temperature (° C.) 260 260 260 (FIG. 8, 10c) Block 4 Temperature (° C.) 260 260 260 (FIG. 8, 10d) H₂ produced/mole of glycerol feed 1.67 1.26 0.72 % Carbon/Carbon in Feed CO₂ 48.9% 44.4% 27.4% CH₄ 14.5% 12.7% 6.1% C₂H₆ 18.9% 16.0% 6.0% C₃H₈ 9.4% 7.4% 4.8% C₄H₁₀ 0.6% 0.7% 0.2% C₅H₁₂ 1.0% 1.0% 0.3% C₆H₁₄ 1.1% 0.7% 0.1% C₆ ⁺ Hydrocarbons in Organic Phase 0.0% 0.4% 5.4% C₂-C₆ Oxygenates in Organic Phase 0.0% 1.7% 7.9% C₂-C₆ Oxygenates in Aqueous Phase 6.9% 13.3% 42.6%

Example 35

A total of 10.61 grams of the 1:2.5 Pt/Re catalyst were loaded into the 8.5 mm stainless steel reactor tube described in Example 4 and the reactor system illustrated in Example 1. The catalyst was reduced with flowing hydrogen at 350° C. for two hours before liquid feed was introduced to the catalyst bed. A 50 wt % glycerol solution containing either 1 ppm or 20 ppm sulfate in water was fed downflow across the reactor at a WHSV of 1.24 grams of glycerol per gram of catalyst per hour. The block heaters were controlled such that the first 10.1 cm of the reactor was held at 260° C., the second 10.1 cm of the reactor was at approximate 306° C., the next 10.1 cm of the reactor was at approximately 355° C., and the last 10.1 cm of the reactor at 400° C. The separator pressure was maintained at 600 psig.

The effluent from the reactor was cooled down with a water cooled condenser, separated in a three-phase separator, and then analyzed as described in Example 5. In this system, there was complete conversion of the glycerol. Table 10 below shows the yields of hydrogen as well as the yields of carbon containing product compounds.

TABLE 10 Yields of Hydrogen and Carbon Containing Products from Example 35 K₂SO₄ loading Sulfate 1 20 Block 1 Temperature (° C.) 260 260 Block 2 Temperature (° C.) 307 305 Block 3 Temperature (° C.) 354 356 Block 4 Temperature (° C.) 400 400 H2 produced/mole of glycerol feed 1.01 0.83 % Carbon/Carbon in Feed CO₂ 42.8% 41.7% CH₄ 15.7% 16.1% C₂H₆ 15.8% 11.9% C₃H₈ 19.9% 18.2% C₄H₁₀ 1.8% 3.0% C₅H₁₂ 2.3% 3.4% C₆H₁₄ 1.0% 1.7% C₆ ⁺ Hydrocarbons in Organic Phase 0.0% 1.1% C₂-C₆ Oxygenates in Organic Phase 0.0% 0.7% C₂-C₆ Oxygenates in Aqueous Phase 0.2% 0.1%

Example 36

A bimetallic catalyst system containing platinum and rhenium (5 wt % platinum with a molar ratio of Pt:Re of 1:5) supported on activated carbon (Calgon UU 60×120 mesh carbon) was prepared using an incipient wetness technique. Activated carbon was added slowly to a 30% hydrogen peroxide solution. After addition of the carbon was completed, the mixture was left overnight. The aqueous phase was decanted and the carbon was washed three times with deionized water, and then dried under vacuum at 100° C. An aqueous solution, with a volume equal to the incipient wetness volume for the carbon to be impregnated and containing dihydrogen hexachloroplatinate (IV) hexahydrate (Alfa Aesar, 39.85% Pt) and perrhemic acid solution (Alfa Aesar, 76.41% HReO₄) was applied drop wise, while stirring, to hydrogen peroxide functionalized carbon. The wetted carbon was then dried at 100° C. under vacuum.

Example 37

11.97 grams of the 1:5 Pt/Re catalyst described in Example 36 were loaded into the 8.5 mm diameter stainless steel tube as described in Example 4 and the reactor system illustrated in Example 1. The catalyst was reduced with flowing hydrogen at 350° C. for two hours before liquid feed was introduced to the catalyst bed. A 57.2 wt % sorbitol solution containing 0 ppm sulfate in water solution was fed downflow across the reactor at a WHSV of 1.20 grams of sorbitol per gram of catalyst per hour. The block heaters were controlled such that the first 10.1 cm of the reactor was held at 260° C., the second 10.1 cm of the reactor was at 260° C., the next 10.1 cm of the reactor was at 360° C., and the last 10.1 cm of the reactor at 410° C. The separator pressure was maintained at 600 psig. The effluent from the reactor was cooled down with a water cooled condenser and separated in a three-phase separator. The product fractions were analyzed as described in Example 5. In addition, the organic phase was collected, separated, and weighed, with a sample sent to Southwest Research Institute (San Antonio, Tex.) for gasoline analysis. In this system, there was complete conversion of the glycerol. Table 11 below shows the yields of hydrogen as well as the yields of carbon containing product compounds.

TABLE 11 Yields of Hydrogen and Carbon Containing Products from Example 37 Block 1 Temperature (° C.) (FIG. 8, 10a) 260 Block 2 Temperature (° C.) (FIG. 8, 10b) 260 Block 3 Temperature (° C.) (FIG. 8, 10c) 360 Block 4 Temperature (° C.) (FIG. 8, 10d) 410 Products moles of H2/mole of Sorbitol feed 1.36 % Carbon/Carbon in Feed CO2 44.37 Methane 9.24 Ethane 8.25 Propane 11.74 Butane 6.53 Pentane 5.66 Hexane 3.79 C7-C13 Normal 0.08 C4-C13 Isoparaffin 0.99 C6-C12 Aromatic 2.45 C8-C11 Naphthalene/Napthenes 0.93 C5-C10 Olefins 0.45 C4-C6 Oxygenated Compounds in Organic Phase 1.68 Oxygenates in Aqueous Phase 3.83

Conversion of Oxygenates to C5+ Compounds Using Acidic Catalysts Example 38

An aqueous 1.0 molar lanthanum nitrate solution was prepared and added to H-mordenite extrudates (BASF 712A-5-2641-1) for a target of 3 weight % La on the catalyst after the subsequent decomposition of the metal precursor. The La solution was mixed briefly with the catalyst and then soaked at 80° C. for 6 hours. The excess liquid was then removed and the catalyst rinsed with deionized water. The catalyst was then dried in a vacuum oven and calcined in air at 550° C. Following this, the catalyst was ground and sieved to restrict the particles sizes to those that were maintained on a 60 mesh screen after passing through an 18 mesh screen.

Example 39

Deionized water was added to H-mordenite extrudates (BASF 712A-5-2641-1, with particle sizes restricted to those that were maintained on a 60 mesh screen after passing through an 18 mesh screen) until extra water covered the support. An aqueous 0.36 molar nickel nitrate solution was then added to the wet support to target 1 weight % Ni after decomposition of the metal precursor. The catalyst was mixed briefly and left to soak for 48 hours. The catalyst was then dried in a vacuum oven and calcined in air at 400° C.

Example 40

An aqueous 1.0 molar europium chloride solution was prepared and added to H-Mordenite (BASF 712A-5-2641-1, with particle sizes restricted to those that were maintained on a 60 mesh screen after passing through an 18 mesh screen) for a target of 3 weight % Eu on the catalyst after the subsequent decomposition of the metal precursors. The Eu solution was mixed briefly with the catalyst and then soaked at 80° C. for 6 hours. The excess liquid was then removed and the catalyst rinsed with deionized water. The catalyst was then dried in a vacuum oven and calcined in air at 550° C. Following this the catalyst was ground and sieved to restrict the particles sizes to those that were maintained on a 60 mesh screen after passing through an 18 mesh screen.

Example 41

H-Beta zeolite extrudates (1.6 mm diameter extrudates) were ground and sieved to restrict the particle sizes to those that were maintained on a 60 mesh screen after passing through an 18 mesh screen. An aqueous gallium nitrate solution was added by incipient wetness to target 1.2 weight % Ga on the catalyst after decomposition of the metal precursor. The catalyst was then dried in a vacuum oven and calcined in air at 400° C.

Example 42

Phosphoric acid was diluted with deionized water and added by incipient wetness to a Davicat SiO₂/Al₂O₃ support (Grace-Davis, with particle sizes restricted to those that were maintained on a 60 mesh screen after passing through an 18 mesh screen) to target 5 weight % phosphorous on the catalyst. The catalyst was then dried in a vacuum oven overnight and subsequently calcined in a stream of flowing air at 500° C.

Example 43

An aqueous nickel nitrate solution was added to an alumina bound ZSM-5 zeolite preparation (SiO₂:Al₂O₃ 30:1, with particle sizes restricted to those that were maintained on a 60 mesh screen after passing through an 18 mesh screen) using an incipient wetness technique to target a nickel loading of 1.0 weight %. The preparation was dried overnight in a vacuum oven and subsequently calcined in a stream of flowing air at 400° C.

Example 44

An aqueous gallium nitrate solution was added to an alumina bound ZSM-5 zeolite preparation (SiO₂:Al₂O₃ 80:1, with particle sizes restricted to those that were maintained on a 60 mesh screen after passing through an 18 mesh screen) using an incipient wetness technique to target a gallium loading of 1.2 weight %. The preparation was dried overnight in a vacuum oven and subsequently calcined in a stream of flowing air at 400° C.

Example 45

Catalyst systems produced using the methods of Examples 38 to 44 were investigated for the vapor-phase condensation of various oxygenates at a temperature from 325° C. to 375° C. and a total pressure between 200 psig and 625 psig, and with WHSVs ranging from 1.9 to 42.8. In these investigations, two different size reactors were used; 15 and 18 milliliters of catalyst were loaded into a 8.5 mm internal diameter stainless steel tube reactor or between 50 and 70 milliliters of catalyst were loaded into a 21.2 mm stainless steel tube reactor (Example 4). The reaction process flow was as described in Example 1 or Example 3 depending on the feedstock, with an analysis completed as described in Example 5.

Operating conditions and results from these experiments are shown in Table 12. Where feed compositions add up to less than 100%, the balance was water. As these results show, a variety of oxygenates, including alcohols and ketones, both 3 carbon and 5 carbon, are substrates which may be converted to C₅+ hydrocarbons across a broad range of conditions. Zeolites are particularly useful in these conversions, as shown by experiments FF, GG, HH, II, JJ, LL, and MM. Experiments FF, GG, HH, II, and JJ show that the main products of alcohol conversion across mordenite and beta zeolites were olefinic condensation products. The phosphorous impregnated silica alumina catalyst, experiment KK, demonstrated a similar product selectivity profile. In contrast, the ZSM-5 based catalysts, Experiments LL and MM, produced significant fractions of aromatic and paraffinic components.

TABLE 12 Vapor Phase Condensation of Oxygenates Over Acid Catalysts Catalyst Ni/30:1 Ga/80:1 La/ Ni/ Eu/ Eu/ 5% Phosphorous/ SiO2:Al₂O₃ SiO2:Al₂O₃ mordenite mordenite mordenite mordenite Ga/Beta Silica-Alumina ZSM-5 ZSM-5 Experiment FF GG HH II JJ KK LL MM Feed Feed J Feed K Feed L Feed K Feed K Feed M Feed K Feed N WHSV wt_(feed)/(wt_(cat) 1.9 2.1 2.2 1.9 3.1 2.7 42.8 2.1 hr) Reactor ° C. 325 350 325 375 375 375 375 375 Temperature Pressure psig 625 625 600 600 600 600 200 625 Reactor Outlet Yield Distribution C⁴⁻ Alkanes wt % of feed 2.9 0.7 3.9 3.6 1.2 1.6 9.6 7.0 carbon C⁴⁻ Olefins wt % of feed 19.5 47.7 11.3 32.9 32.5 73.5 10.8 0.5 carbon Total C⁴⁻ wt % of feed 22.3 48.4 15.3 36.5 33.7 75.1 20.5 7.5 Hydrocarbons carbon C₅₊ Paraffins wt % of feed 6.6 0.8 16.9 3.1 4.3 1.9 29.6 8.5 carbon C₅₊ Olefins wt % of feed 56.2 46.9 43.1 56.6 52.0 18.4 21.7 0.1 carbon Naphthenes wt % of feed 0.0 2.5 1.5 5.6 3.2 3.4 2.7 1.0 carbon Aromatics wt % of feed 0.0 0.0 1.4 0.0 2.0 0.0 18.0 79.1 carbon Other C₅₊ wt % of feed 0.8 0.1 5.7 1.5 0.2 0.0 7.1 0.0 Hydrocabons carbon Total C₅₊ wt % of feed 63.6 50.3 68.6 66.7 61.8 23.7 79.2 88.6 Hydrocarbons carbon Feed J - 50% 2-pentanol Feed K - 50% isopropyl alcohol Feed L - 59% 2-pentanol Feed M - 90% isopropyl alcohol Feed N - 89.6% Acetone

Production of C5+ Compounds from Oxygenated Hydrocarbons Example 46

A catalyst preparation technique identical to that of Example 44 was followed with the exception that the alumina bound ZSM-5 material had a SiO₂:Al₂O₃ ratio of 30:1.

Example 47

A catalyst produced using the method of Example 46 was investigated for the vapor-phase condensation of a mixture of oxygenates at 375° C. and 200 psig. In this investigation, 11.3 grams of catalyst were loaded into a 8.5 mm internal diameter stainless steel tube reactor as described in Example 4. The reaction process flow was as described in Example 3. The oxygenate mix included, by weight, 25% 2-pentanone, 20% 3-pentanone, 20% 2-pentanol, 10% isopropyl alcohol, 10% valeric acid, 5% 2-methyl tetrahydrofuran. This mixture was added using one pump in the Example 3 reactor system while the second pump added water so that the total combined feed contained 60 weight % water and 40 weight % of mixed oxygenates.

The process was monitored for a period of 128 hours, with samples periodically removed from the system to analyze the process performance. Each analysis was completed as described in Example 5. FIG. 15 shows the fraction of feed carbon that exited the reactor system as C₅₊ compounds as a function of time. FIG. 16 shows the fraction of feed carbon that exited the reactor system as an aromatic hydrocarbon as a function of time. FIG. 14 shows the fraction of feed carbon that exited the reactor system as oxygenates as a function of time.

As FIGS. 14, 15 and 16 show, the catalyst system is able to operate for extended periods of time with an oxygenate mix that contains a mixture of oxygenates, including alcohols, ketones, an acid, and a tetrahydrofuran. Over time the production of C₅+ compounds remains relatively stable, while the amount of aromatic hydrocarbons present in the product drops and the breakthrough of oxygenated compounds increases (FIG. 14). It is believed that the catalyst deactivation is primarily due to the accumulation of carbonaceous deposits limiting the accessibility of the reactants to the active sites.

Example 48

An aqueous solution of hexachloroplatinic acid and perrhenic acid was added to a carbon catalyst support (OLC-AW, Calgon, with particle sizes restricted to those that were maintained on a 50 mesh screen after passing through an 120 mesh screen) using an incipient wetness technique to target a platinum loading of 1.8% and a rhenium loading of 6.3% on the catalyst after subsequent decomposition of the metal precursors. The preparation was dried overnight in a vacuum oven and subsequently reduced in a stream of flowing hydrogen at 400° C. After being reduced the catalyst was stored in a nitrogen atmosphere until ready for use.

Example 49

A catalyst preparation technique identical to that of Example 44 was followed with the exception that the alumina bound ZSM-5 material had a SiO₂:Al₂O₃ ratio of 150:1.

Example 50

Hexachloroplatinic acid and perrhenic acid dissolved in water were added to a monoclinic zirconia catalyst support (NorPro Saint Gobain, product code SZ31164, with particle sizes restricted to those that were maintained on a 60 mesh screen after passing through an 18 mesh screen) using an incipient wetness technique to target a platinum loading of 1.8% and a rhenium loading of 6.3% on the catalyst after subsequent decomposition of the metal precursors. The preparation was dried overnight in a vacuum oven and subsequently calcined in a stream of flowing air at 400° C.

Example 51

The same procedure used for preparing the catalyst of Example 50 was followed with the exception that the target rhenium loading was 1.8%.

Example 52

An 80:1 SiO₂:Al₂O₃ ratio ZSM-5 zeolite (Zeolyst International, CBV 8014) was mixed with a 1:1 molar ratio of ZnO and Al₂O₃ powders so that the ZnO and Al₂O₃ (Dispal 18N4-80, Sasol North America, Houston, Tex.) combined comprised 30 weight % of the total solids. Dilute nitric acid was added at a level of 2 weight % HNO₃ to the combined ZnO and Al₂O₃. The dough consistency was adjusted with water addition to form a workable dough suitable for extrusion and the mixture was extruded using a laboratory scale extruder. The extrudates were dried overnight under vacuum at 100° C. and subsequently calcined at 600° C. under flowing air.

Example 53

An aqueous solution of gallium nitrate was added to the material of Example 52, with particle sizes restricted to those that were maintained on a 60 mesh screen after passing through an 18 mesh screen, using an incipient wetness technique to target a gallium loading of 1.2 weight %. The preparation was dried overnight in a vacuum oven and subsequently calcined in a stream of flowing hydrogen at 400° C.

Example 54

An aqueous solution of nickel nitrate was added to the material of Example 52, with particle sizes restricted to those that were maintained on a 60 mesh screen after passing through an 18 mesh screen, using an incipient wetness technique to target a nickel loading of 1.0 weight %. The preparation was dried overnight in a vacuum oven and subsequently calcined in a stream of flowing hydrogen at 400° C.

Example 55

The catalyst systems referenced in Examples 6, 46, 48, 49, 51, 53, and 54 were investigated for the conversion of glycerol, sorbitol, sucrose, and xylose to hydrocarbons using the reactor configuration described in Example 2. The studies were conducted using two 21.2 mm internal diameter stainless steel tube reactors shown in Example 4, with an analysis completed as described in Example 5. Tungstated zirconia (NorPro-Saint Gobain, product code SZ61143, with particle sizes restricted to those that were maintained on a 60 mesh screen after passing through an 18 mesh screen) was placed on top of the condensation catalyst installed in the second reactor to provide for a zone for vaporization of the first reactor effluent prior to entering the condensation catalyst.

Table 13 shows the results of these investigations. For Experiment NN (38% Sucrose+7% Xylose), a stream of hydrogen with a targeted flow rate equal to 3 times the moles of sucrose plus 1.5 times the moles of xylose was combined with the feed prior to entering the reactor. The other experiments were conducted without externally supplied hydrogen. Heaters external to the reactor, shown in FIG. 9 as 10 a, 10 b, 10 c, 10 d, 23 a, 23 b, 23 c, and 23 d, were used to maintain the reactor wall temperatures, as indicated in Table 13. The hydrocarbon products of these studies, disclosed in Table 13, were grouped into a C⁴⁻ fraction, which are predominately present in the gas phase at ambient temperature and pressure, and a C₅₊ fraction, which are generally suitable for incorporation into liquid fuels. The results show that a variety of sugars and polyhydric alcohols may be readily converted to C₅₊ hydrocarbons by the processes described here. The products contained mainly paraffin and aromatic constituents. The breakdown of paraffins and aromatics within this

TABLE 13 Conversion of Sugars and Polyhydric Alcohols to C5+ Hydrocarbons Experiment NN OO PP QQ Catalyst Descriptions Hydrogenation Example 6 None None None APR/Deoxygenation Example 48 Example 51 Example 51 Example 50 Condensation Example 49 Example 53 Example 46 Example 54 Catalyst Loadings Hydrogenation grams 10 — — — APR/Deoxygenation grams 40 52 60 60 Tungstated Zirconia grams 71 60 ~60 58 Condensation grams 62 60 60 60 Heater Block Temperature Ranges, Inlet of Catalyst Bed-Outlet of Catalyst Bed Hydrogenation ° C. 100-150 — — — APR/Deoxygenation ° C. 245-265 250-270 335-365 275-285 Tungstated Zirconia ° C. 250-375 370-370 395-375 395-375 Condensation ° C. 375-375 385-385 375-375 375-375 Pressures First Reactor Outlet psig 625 625 625 625 2nd Reactor Outlet psig 625 350 250 350 Feed Feed O Feed P Feed P Feed Q Hydrogen production mol/mol feed −2.85 0.73 0.57 0.50 WHSV wt_(feed)/(wt_(cat) hr) 1.6 1.9 2.0 2.0 Reactor Outlet Yield Distribution C⁴⁻ Alkanes wt % of feed carbon 21.2 26.9 8.1 13.0 C⁴⁻ Olefins wt % of feed carbon 1.1 1.4 1.3 5.2 Total C⁴⁻ Hydrocarbons wt % of feed carbon 22.3 28.3 9.4 18.1 C₅₊ Paraffins wt % of feed carbon 20.0 7.9 9.5 11.3 C₅₊ Olefins wt % of feed carbon 0.8 1.9 1.2 7.8 Naphthenes wt % of feed carbon 1.9 1.4 1.6 1.2 Aromatics wt % of feed carbon 25.0 17.8 48.4 22.3 Other C₅₊ Hydrocarbons wt % of feed carbon 0.0 1.1 0.2 3.4 Total C₅₊ Hydrocarbons wt % of feed carbon 47.7 30.1 61.0 46.1 Feed O - 38% Sucrose, 7% Xylose Feed P - 50% Glycerol Feed Q - 50% Sorbitol

Example 56

The process described in Example 55 and exemplified by Experiment QQ in Table 13 was operated for a period of more than 400 hours. After an initial period of time in operation, the conversion to aromatic components and the yield of hydrocarbons dropped, shown in FIGS. 18 and 19 as Cycle 1. In FIG. 18, the heating value of C₅₊ hydrocarbons present at the outlet of the second reactor, as a percentage of the heating value of the feed, is shown. In FIG. 19, the carbon present as aromatic hydrocarbons at the outlet of the second reactor is shown as a percentage of the carbon present in the feed. After approximately 120 hours on stream, the second reactor was bypassed while the first reactor continued operating. An oxidative regeneration of the catalyst in the second reactor was then performed. During the regeneration, a flow of nitrogen and air was initiated so that the target oxygen concentration at the second reactor inlet was 1 mol %. The second reactor block temperatures were then raised to 500° C. and the flow of nitrogen and oxygen continued until carbon dioxide was no longer detected at the second reactor outlet. The oxygen concentration was then raised to a target level of 5 mol %. This flow was continued until carbon dioxide was no longer detected at the second reactor outlet. At this time the oxygen flow was discontinued while the nitrogen flow continued. The second reactor block temperatures were then reduced to 400° C. while the composition of the gas flowing through the catalyst bed was changed to hydrogen. The second reactor block temperatures were then adjusted to those shown for Experiment QQ in Table 13. The second reactor was then placed back on line, targeting the conditions shown for Experiment QQ in Table 13. The second reactor was then subjected to multiple cycles of operation and regeneration, with the results for the period of time in operation shown in FIGS. 18 and 19. As these results show, the regeneration of the condensation catalyst resulted in a restoration of activity, consistent with the theory that deposition of carbonaceous materials were the main cause of a drop in catalyst performance over time. Furthermore, the results show that the condensation catalyst may be regenerated multiple times without a significant loss of performance.

Preparation of Gasoline Compositions Example 57

A gasoline composition (gasoline composition GC1) was prepared by admixing a base gasoline with 5% vol., based on the volume of the final gasoline composition, of the product of the process described in Example 55 and exemplified by Experiment PP in Table 13.

The base gasoline used and the gasoline composition prepared are detailed in Table 14.

Example 58

A gasoline composition (gasoline composition GC2) was prepared by admixing a base gasoline with 10% vol., based on the volume of the final gasoline composition, of the product of the process described in Example 55 and exemplified by Experiment OO in Table 13.

The base gasoline used and the gasoline composition prepared are detailed in Table 14.

TABLE 14 Property Unit Base Gasoline GC1 GC2 RVP kPa 92.9 88.7 85.8 Density Kg/m³ 727.5 735.2 736.6 IBP ° C. 26.9 27.6 27.6 FBP ° C. 194.3 206.8 198.2 Residue % v 1 1.2 1.1 Recovery % v 95.9 95.8 958 Loss % v 3.1 3 3.1 T10 ° C. 39.9 40.2 41.2 T20 ° C. 51 51.5 52.8 T30 ° C. 63.4 64.3 65.9 T40 ° C. 76.4 78.4 79.8 T50 ° C. 89.9 92.5 94.2 T60 ° C. 102.6 106 107.4 T70 ° C. 114.8 118.8 120.1 T80 ° C. 129 134 136.1 T90 ° C. 149 154.1 155.6 T95 ° C. 165 170.4 171 E70 % v 35.1 34.1 32.9 E100 % v 57.9 55.3 54 E120 % v 74 70.7 69.8 E150 % v 90 88 87 E180 % v 97.5 96.6 96.7 RON 95.6 96.4 96.3 MON 85.4 85.5 85.1

It can be seen from the information presented in Table 14 above that the gasoline compositions comprising the products prepared by the process described in Example 55 have very similar distillation characteristics to the base gasoline, and advantageously have a higher Road Octane Number (RON) than the base gasoline. It can also be seen from the information presented in Table 14 above that the gasoline compositions comprising the products prepared by the process described in Example 55 have a lower Reid Vapour Pressure (RVP) compared to the base gasoline, which may advantageously be used to decrease the RVP of a gasoline in order to meet specific requirements of the gasoline composition, or alternatively allow the addition of greater amounts of gasoline components whose addition to gasoline compositions may have been limited due to the volatility of such components.

Example 59

Two separate gasoline compositions were prepared using sorbitol and sucrose as a feedstock, and then analyzed for their carbon 14 (14C) concentration as compared to petroleum-based gasoline.

The first gasoline sample (V-18510) was produced from a 50% solution of sorbitol in water using a reactor system similar to that described in Example 55, except that the system included a second condensation reactor in a lead/lag configuration. The APR/deoxygenation catalyst was prepared as described in Example 50, while the condensation catalyst was prepared as described in Example 43. Multiple runs using the sorbitol feedstock where conducted over various temperatures and conditions. APR/deoxygenation reactions were conducted in a single reactor over a low to high temperature profile with temperatures varied from 110° C. to 130° C. at the inlet and from 235° C. to 250° C. at the outlet. Condensation reactions were conducted in a two reactor system with the temperature in the lead reactor varied from 345° C. to 385° C. and the lag reactor varied from 260° C. to 385° C. Pressure conditions were also varied from 620 psig to 630 psig for the APR/deoxygenation reactions and 95 psig to 105 psig for the condensation reactions. WHSV was varied from 0.9 to 1.1 hr-1 for the APR/deoxygenation catalyst.

A second gasoline sample (V-18512) was prepared from a collective sample of gasoline produced from sucrose using a reactor system as illustrated in FIG. 6. Sucrose was fed at various temperatures, pressures and WHSV over a hydrogenation catalyst containing 2.5% ruthenium on UU carbon (Calgon, with particle sizes restricted to those that were maintained on a 120 mesh screen after passing through a 60 mesh screen), and the APR/deoxygenation catalyst and condensation catalyst described above for the sorbitol feed. Conditions for the hydrogenation reaction varied with temperatures in the range of 115° C. to 140° C., and pressures in the range of 620 psig to 680 psig. The WHSV, temperature and pressure conditions for the APR/deoxygenation were as described for sorbitol. The condensation reaction was conducted in a single condensation reactor with the WHSV, temperature and pressure conditions the same as that described above for the lead reactor.

The product streams from the various runs of sorbitol were combined into a single sample (V-18510) and then subjected to a distillation step as described in Example 29. The product streams from the various runs of sucrose were also combined into a single sample (V-18512) and then subjected to distillation as described in Example 29. Distillation fractions having a boiling point of less than 210° C. were collected for further blending into final fuel compositions. A sample of each fraction was also collected for 14C testing.

Carbon 14 testing was performed by Beta Analytical Inc (Miami, Fla. USA) using ASTM-D6866, Test Methods for Determining the Biobased Content of Natural Range Materials Using Radiocarbon and Isotope Ratio Mass Spectrometry Analysis. In addition to 14C testing on samples V-18510 and V-18512, a biobased determination was also performed on two additional samples collected from separate retail gas stations in Madison, Wis. The first sample (V-RRGWE) was a regular unleaded gasoline identified as containing up to 10% ethanol, while the second sample (V-SVPNE) was premium gasoline. The results of the study are listed in Table 15 below.

Mean Percentage of Sample No. ASTM-D6866 Method Biobased Material V-18510 Method - B 99% V-18512 Method - B 99% V-RRGWE Method - B 7% V-SVPNE Method - B 2% 

We claim:
 1. A moderate fraction of a carbohydrate derived component having at least one C₄₊ compound, wherein: the moderate fraction exhibits: a mean percentage of 99% or more biobased material, as determined by C₁₄ testing; and, a final boiling point in the range of from 200 to 320° C.; and, the moderate fraction comprises: a first quantity of one or more branched carbohydrate derived C₄₊ alkanes; a second quantity of one or more straight chain carbohydrate derived C₄₊ alkanes; a concentration of one or more substituted carbohydrate derived C₅₊ cycloalkanes comprising substituents selected from the group consisting of branched C₃₋₄ alkyls and straight chain C₁₋₄ alkyls, at least some of the substituted carbohydrate derived C₅₊ cycloalkanes comprising fused cycloalkanes.
 2. The moderate fraction of claim 1 exhibiting a freeze point of −40° C. or lower.
 3. The moderate fraction of claim 1 exhibiting a freeze point of −47° C. or lower.
 4. The moderate fraction of claim 1 exhibiting a density at 15° C. in the range of from 700 to 890 kg/m³.
 5. The moderate fraction of claim 1 exhibiting a density at 15° C. in the range of from 730 to 840 kg/m³.
 6. The moderate fraction of claim 1 wherein the one or more substituted carbohydrate derived C₅₊ cycloalkanes further comprise substituents selected from the group consisting of branched C₃₋₄ alkylenes and straight chain C₁₋₄ alkylenes.
 7. The moderate fraction of claim 1 wherein the moderate fraction further comprises one or more carbohydrate derived aromatics.
 8. The moderate fraction of claim 7 comprising a total aromatics content of at most 30% vol.
 9. The moderate fraction of claim 1 derived by a method comprising: (a) providing water and carbohydrate derived water-soluble oxygenated hydrocarbon comprising C₁₊O₁₊ hydrocarbon in an aqueous liquid phase and/or a vapor phase; (b) providing H₂; (c) catalytically reacting in the liquid and/or vapor phase the carbohydrate derived water-soluble oxygenated hydrocarbon with the H₂ in the presence of a deoxygenation catalyst at a deoxygenation temperature and deoxygenation pressure to produce carbohydrate derived oxygenate comprising C₁₊O₁₋₃ hydrocarbon in a reaction stream; (d) catalytically reacting in the liquid and/or vapor phase the carbohydrate derived oxygenate in the presence of a condensation catalyst at a condensation temperature of from 250° C. to 325° C. and a condensation pressure of 600 psig or more to produce the carbohydrate derived component having at least one C₄₊ compound; and, (e) separating the moderate fraction of the carbohydrate derived component having at least one C₄₊ compound.
 10. A kerosene composition comprising: a moderate fraction of a carbohydrate derived component having at least one C₄₊ compound having a mean percentage of 99% or more biobased material, as determined by C₁₄ testing, the moderate fraction having a final boiling point in the range of from 200 to 320° C.; the moderate fraction comprising: a first quantity of one or more branched carbohydrate derived C₄₊ alkanes; a second quantity of one or more straight chain carbohydrate derived C₄₊ alkanes; a concentration of one or more substituted carbohydrate derived C₅₊ cycloalkanes comprising substituents selected from the group consisting of branched C₃₋₄ alkyls and straight chain C₁₋₄ alkyls, at least some of the substituted carbohydrate derived C₅₊ cycloalkanes comprising fused cycloalkanes; the kerosene composition having a final boiling point in the range of from 200 to 320° C. and a viscosity at −20° C. in the range of from 0.8 to 10 cSt (ASTM D445).
 11. The kerosene composition of claim 10 wherein the moderate fraction exhibits a freeze point of −40° C. or lower.
 12. The kerosene composition of claim 10 wherein the moderate fraction exhibits a freeze point of −47° C. or lower.
 13. The kerosene composition of claim 10 wherein the moderate fraction exhibits a density at 15° C. in the range of from 775 to 845 kg/m³.
 14. The kerosene composition of claim 10 wherein the moderate fraction exhibits a density at 15° C. in the range of from 780 to 830 kg/m³.
 15. The kerosene composition of claim 10 wherein the one or more substituted carbohydrate derived C₅₊ cycloalkanes further comprise substituents selected from the group consisting of branched C₃₋₄ alkylenes and straight chain C₁₋₄ alkylenes.
 16. The kerosene composition of claim 10, wherein the moderate fraction further comprises one or more carbohydrate derived aromatics.
 17. The kerosene composition of claim 16 wherein the total aromatics content is at most 30% vol.
 18. The kerosene composition of claim 10 further comprising one or more different kerosene blend components selected from the group consisting of petroleum derived product streams, Fischer-Tropsch derived product streams, biofuel components, and combinations thereof.
 19. The kerosene composition of claim 9 further comprising one or more different kerosene blend components selected from the group consisting of derivatives of esters and carboxylic acids.
 20. The kerosene composition of claim 16 further comprising one or more different kerosene blend components comprising one or more carbohydrate derived aromatics.
 21. The kerosene composition of claim 10 comprising from about 0.1 to about 90% vol. of the moderate fraction.
 22. The kerosene composition of claim 10 comprising at most 0.01 wt. % sulfur.
 23. The kerosene composition of claim 10 comprising no more than 50 ppmw sulfur.
 24. The kerosene composition of claim 10 comprising no more than 15 ppmw sulfur.
 25. The kerosene composition of claim 10 wherein the moderate fraction is derived by a method comprising: (a) providing water and carbohydrate derived water-soluble oxygenated hydrocarbon comprising C₁₊O₁₊ hydrocarbon in an aqueous liquid phase and/or a vapor phase; (b) providing H₂; (c) catalytically reacting in the liquid and/or vapor phase the carbohydrate derived water-soluble oxygenated hydrocarbon with the H₂ in the presence of a deoxygenation catalyst at a deoxygenation temperature and deoxygenation pressure to produce carbohydrate derived oxygenate comprising C₁₊O₁₋₃ hydrocarbon in a reaction stream; (d) catalytically reacting in the liquid and/or vapor phase the carbohydrate derived oxygenate in the presence of a condensation catalyst at a condensation temperature of from 250° C. to 325° C. and a condensation pressure of 600 psig or more to produce the carbohydrate derived component having at least one C₄₊ compound; and, (e) separating the moderate fraction of the carbohydrate derived component having at least one C₄₊ compound.
 26. The kerosene composition of claim 25 wherein the condensation catalyst is selected from the group consisting of an acid condensation catalyst and an acid-base condensation catalyst.
 27. The kerosene composition of claim 25 wherein the condensation catalyst comprises a ZSM-5 type zeolite.
 28. A kerosene composition comprising: a moderate fraction of a carbohydrate derived component having at least one C₄₊ compound having a mean percentage of 99% or more biobased material, as determined by C₁₄ testing, the moderate fraction having a final boiling point in the range of from 200 to 320° C.; the moderate fraction comprising: a first quantity of one or more branched carbohydrate derived C₄₊ alkanes; a second quantity of one or more straight chain carbohydrate derived C₄₊ alkanes; a concentration of one or more substituted carbohydrate derived C₅₊ cycloalkanes comprising substituents selected from the group consisting of branched C₃₋₄ alkyls and straight chain C₁₋₄ alkyls, at least some of the substituted carbohydrate derived C₅₊ cycloalkanes comprising fused cycloalkanes; one or more different kerosene blend components comprising a synthetic paraffin comprising components having boiling points within the range of from 110 to 320° C.; the kerosene composition having a final boiling point in the range of from 200 to 320° C. and a viscosity at −20° C. in the range of from 0.8 to 10 cSt (ASTM D445).
 29. The kerosene composition of claim 28 wherein the one or more different kerosene blend components are selected from the group consisting of a Fischer-Tropsch product, a synthetic paraffin derived from a synthesis product of a Fischer Tropsch condensation process.
 30. The kerosene composition of claim 28 exhibiting a freeze point of −40° C. or lower.
 31. The kerosene composition of claim 28 exhibiting a freeze point of −47° C. or lower.
 32. The kerosene composition of claim 28 wherein the one or more substituted carbohydrate derived C₅₊ cycloalkanes further comprise substituents selected from the group consisting of branched C₃₋₄ alkylenes and straight chain C₁₋₄ alkylenes.
 33. The kerosene composition of claim 28 wherein the moderate fraction further comprises one or more carbohydrate derived aromatics.
 34. The kerosene composition of claim 33 wherein the total aromatics content is at most 30% vol.
 35. The kerosene composition of claim 28 wherein the one or more different kerosene blend components further comprise components selected from the group consisting of petroleum derived product streams, biofuel components, and combinations thereof.
 36. The kerosene composition of claim 28 wherein the one or more different kerosene blend components are selected from the group consisting of derivatives of esters and carboxylic acids.
 37. The kerosene composition of claim 28 wherein the one or more different kerosene blend components further comprise one or more carbohydrate derived aromatics.
 38. The kerosene composition of claim 28 wherein the moderate fraction exhibits a density at 15° C. in the range of from 775 to 845 kg/m³.
 39. The kerosene composition of claim 28 wherein the moderate fraction exhibits a density at 15° C. in the range of from 780 to 830 kg/m³.
 40. The kerosene composition of claim 28 comprising from about 0.1 to about 90% vol. of the moderate fraction.
 41. The kerosene composition of claim 28 comprising at most 0.01 wt. % sulfur.
 42. The kerosene composition of claim 28 comprising no more than 50 ppmw sulfur.
 43. The kerosene composition of claim 28 comprising no more than 15 ppmw sulfur.
 44. The kerosene composition of claim 28 wherein the moderate fraction is derived by a method comprising: (a) providing water and carbohydrate derived water-soluble oxygenated hydrocarbon comprising C₁₊O₁₊ hydrocarbon in an aqueous liquid phase and/or a vapor phase; (b) providing H2; (c) catalytically reacting in the liquid and/or vapor phase the carbohydrate derived water-soluble oxygenated hydrocarbon with the H2 in the presence of a deoxygenation catalyst at a deoxygenation temperature and deoxygenation pressure to produce carbohydrate derived oxygenate comprising C₁₊O1⁻³ hydrocarbon in a reaction stream; (d) catalytically reacting in the liquid and/or vapor phase the carbohydrate derived oxygenate in the presence of a condensation catalyst at a condensation temperature of from 250° C. to 325° C. and a condensation pressure of 600 psig or more to produce the carbohydrate derived component having at least one C₄₊ compound; and, (e) separating the moderate fraction of the carbohydrate derived component having at least one C₄₊ compound. 